Removing carbon dioxide from waste streams through co-generation of carbonate and/or bicarbonate minerals

ABSTRACT

Methods for removing carbon dioxide and other pollutants from a gas stream are provided. The methods include obtaining hydroxide in an aqueous mixture, mixing the hydroxide with the gas stream to produce bicarbonate products or a combination of carbonate and bicarbonate products in an admixture, separating the products from the admixture, and using the products to perform ion-exchanges with one or more group-1 or group-2 salts to precipitate carbonates, wherein obtaining the hydroxide comprises obtaining a group-1 or group-2 salt; mixing the salt with acid and water, acid and steam, or acid, water, and steam to produce a protonated brine solution; and electrolyzing the protonated brine solution to produce a hydroxide; and wherein mixing the hydroxide with the gas stream comprises altering the product equilibrium to favor the production of bicarbonate products.

CROSS-REFERENCES TO RELATED APPLICATIONS

The present application is a continuation of application Ser. No. 11/233,509, filed Sep. 22, 2005, entitled “Removing Carbon Dioxide from Waste Streams through Co-Generation of Synthetic Carbonate Minerals,” now U.S. Pat. No. 7,727,374, which claims priority to U.S. Provisional Patent Application Ser. No. 60/718,906, filed Sep. 20, 2005; U.S. Provisional Patent Application Ser. No. 60/642,698, filed Jan. 10, 2005; and U.S. Provisional Patent Application Ser. No. 60/612,355, filed Sep. 23, 2004. The entire text of each of the above-referenced disclosures (including the appendices) is specifically incorporated by reference herein without disclaimer.

BACKGROUND OF THE INVENTION

1. Field of the Invention

The present invention generally relates to the field of removing carbon dioxide and, collaterally with that removal, other pollutants from waste streams. More particularly, the present invention relates to removing carbon dioxide and other pollutants from waste streams through the absorption of carbon dioxide and other pollutants from concentrated flue-gas-like streams and then the co-generation of carbonate and/or bicarbonate materials that entrain and neutralize any incidental pollutants absorbed.

2. Related Art

Considerable domestic and international concern in both private and commercial sectors has been increasingly focused over the last four decades on emissions from industries into the air. In particular, attention has been focused on the greenhouse gases that have the property of affecting the retention of solar heat in the atmosphere, producing the “greenhouse effect.” The greenhouse effect occurs when incoming heat from the sun is trapped in the atmosphere and hydrosphere of the earth, raising the average atmospheric temperature, ocean temperature, and other mean and average temperature measures of planet Earth, up to and including the point of climatic change; the effect is generally agreed as an operating effect in the Earth's thermal balance, though the rates, the extent to which man's combustion of materials affects it and the extent, direction, and magnitude of the effect are debated. Despite the degree of debate, all would agree there is a benefit to removing CO₂ (and other chemicals) from point-emission sources if the cost for doing so were sufficiently small.

Greenhouse gases are predominately made up of carbon dioxide and are produced by municipal power plants and large-scale industry in site-power-plants, though they are also produced in any normal carbon combustion (such as automobiles, rain-forest clearing, simple burning, etc.), though their most concentrated point-emissions occur at power-plants across the planet, making reduction or removal from those fixed sites an attractive point to effect a removal-technology. Because energy production is a primary cause of greenhouse gas emissions, methods such as reducing carbon intensity, improving efficiency, and sequestering carbon from power-plant flue-gas by various means has been researched and studied intensively over the last thirty years.

Reducing carbon intensity involves the alternate use of non-carbon energy sources such as nuclear, hydroelectric, photovoltaic, geothermal, and other sources of electric power to reduce the percentage of power produced through exclusive carbon combustion. While each of these techniques of power-generation continues to gain in terms of total energy production, the projections of world electricity demand are expected to increase at rates faster than energy production from these methods. Therefore, carbon greenhouse gas emissions are expected to increase despite growth in non-carbon energy sources.

Improving efficiency has generally focused on techniques of improving the combustion of carbon through pre-combustion, decarbonization, oxygen-fired combustion, etc. by first decreasing the amount of CO₂ produced and then oxidizing all potential pollutants as completely as possible. Also, the technique increases the amount of energy generated per carbon dioxide emission released for improved efficiency. While strides in this area have improved combustion efficiency, there is little more improvement to be extracted from this field of endeavor.

Attempts at sequestration of carbon (in the initial form of gaseous CO₂) have produced many varied techniques, which can be generally classified as geologic, terrestrial, or ocean systems. These techniques are primarily concerned with transporting generated carbon dioxide to physical sites and injecting the carbon dioxide into geologic, soil, or ocean repositories. Each of these sequestering techniques involves large costs in preparing CO₂ for transport, accomplishing the transport, and performing the injection into a “carbon bank.” As such, these techniques are generally not economically feasible and in many cases consume more energy than the original carbon produced.

Sequestration can also include several industrial processes which include scrubbing, membranes, lower-cost O₂, and hydrates. However, each of these technologies suffer due to the capital plant costs raised to uneconomic levels, and the effect of CO₂ capture on the cost of electricity is prohibitive.

The referenced shortcomings are not intended to be exhaustive, but rather are among many that tend to impair the effectiveness of previously known techniques for removing carbon dioxide from waste streams; however, those mentioned here are sufficient to demonstrate that the methodologies appearing in the art have not been altogether satisfactory and that a significant need exists for the techniques described and claimed in this disclosure.

SUMMARY

The present invention provides methods and apparatuses for removing carbon dioxide from waste streams, which methods and apparatuses overcome the problems described above. In general, the invention relates to methods of removing carbon dioxide from a gas stream using a hydroxide compound to form a carbonate and/or bicarbonate. The carbonate and/or bicarbonate can then be employed in any number of uses, or simply discarded.

Various embodiments of the present invention provide advantages over current technologies for filtering carbon dioxide from waste streams. Some potential advantages that are realizable by the invention include the following.

Unlike processes that physically remove the carbon to a remote site, the co-generation at industrial scale of sodium carbonates and/or bicarbonates from sodium chloride and carbon dioxide by synthesis directly converts the undesirable carbon dioxide into chemicals at the point of power-generation, potentially eliminating transportation costs to a sequestration site.

Unlike other efforts at decarbonation of flue-gas streams that are not amenable to retrofitting, embodiments of the present invention may be retrofitted to existing power-plants, greatly lowering the capital costs necessary to implement decarbonation processing. Additionally, the decarbonation processing is scaleable and can be implemented by pilot-to-intermediate-to-full-scale implementation by the addition of incremental reactor units.

Unlike other processes in the art, the decarbonation process of certain embodiments sequesters carbon-dioxide into economically useful chemicals and co-incidentally produces useful by-products such as chlorine gas, sodium carbonate, and hydrogen gas. Because the by-products of the decarbonation process are economically useful, those values offset the costs of sequestration, and in properly designed systems, potentially make the sequestration process profitable in itself.

Due to the co-incidental process of aggressive scrubbing of emitted flue-gases, other undesirable acidic pollutants such as SO_(X), NO_(X), HgO_(X), and others are aggressively scrubbed in the process. Additionally, the scrubbing process can lead to the entrapment and/or entrainment of other gas stream components and/or contaminants in the sodium carbonate (e.g., ash from coal, etc.), thereby removing them from the gas stream.

Particular embodiments of the present invention comprise a method of removing carbon dioxide from a gas stream comprising: obtaining a hydroxide in an aqueous mixture; admixing the hydroxide with the gas stream to produce carbonate products (defined as products containing the carbonate group, CO₃), bicarbonate products (defined as products containing the bicarbonate group, HCO₃), or a mixture of carbonate and bicarbonate products in an admixture; and separating said carbonate and/or bicarbonate products from the admixture, thereby removing carbon dioxide from the gas stream. The hydroxide can be any form of hydroxide, including but not limited to sodium hydroxide, potassium hydroxide, calcium hydroxide, magnesium hydroxide, and aluminum hydroxide. Those of ordinary skill will understand that it is possible to obtain similar chemistry and decarbonation with any number of hydroxides or mixtures of hydroxides. In some preferred embodiments, the hydroxide is a sodium hydroxide.

In certain embodiments, the method further comprises process-controlling the method to produce substantially only carbonate products or substantially only bicarbonate products. In other embodiments, the method further comprises process-controlling the method to produce a mixture of carbonate and bicarbonate products, which mixture can be comprised of about X % carbonate and about Y % bicarbonate, with X-Y combinations being any of the following: 1-99, 2-98, 3-97, 4-96, 5-95, 6-94, 7-93, 8-92, 9-91, 10-90, 15-85, 20-80, 25-75, 30-70, 35-65, 40-60, 45-55, 50-50, 55-45, 60-40, 65-35, 70-30, 75-25, 80-20, 85-15, 90-10, 91-9, 92-8, 93-7, 94-6, 95-5, 96-4, 97-3, 98-2, or 99-1.

In certain embodiments, the admixing occurs in two separate chambers, with one chamber being used to produce carbonate products and the other chamber being used to produce bicarbonate products. In other embodiments, the admixing occurs in a bubble column or series of bubble columns In still other embodiments, separation of carbonate and/or bicarbonate products from the admixture involves a heated-precipitation separation process. In some embodiments, the heat for the separation process is derived from heat exchange with incoming flue-gases. The separated carbonate may be in the form of an aqueous slurry or as a solution of hydroxide, carbonate, and water at various concentrations at the time of separation, and if so, it can then be dried by any of a number of methods. In some embodiments, the carbonate need not be dried. For example, a slurry of sodium carbonate can be used in treatment of hard water. Of course, those of skill will know a wide variety of uses to which the carbonate produced via the methods of the invention can be put, for example, slurry mixtures of sodium bicarbonate and sodium carbonate can be slurried to tank-car for use in various forms of detergent manufacture, in glass manufacture as a flux, etc., as well as the previously-mentioned water-treatment uses.

In certain embodiments, the method further comprises transporting the carbonate products to a remote sequestration site; combining the carbonate products with acid in a neutralization reaction to generate pure carbon dioxide; and injecting the carbon dioxide into a carbon bank. In other embodiments, other components of the gas stream are neutralized and/or entrained/captured in the carbonate-formation process, including SO_(X), NO_(X), and mercuric-containing material.

In some embodiments, obtaining the hydroxide comprises: obtaining a salt; admixing the salt with water, steam, or both to produce a solution; and electrolyzing the solution to produce a hydroxide. In certain embodiments, the solution is electrolyzed using a voltage greater than or equal to about 5 volts, while in other embodiments the solution is electrolyzed using a voltage less than about 5 volts. In some embodiments, the solution is electrolyzed using a voltage between 1 volt and 5 volts, including about 1.5 volts, about 2.0 volts, about 2.5 volts, about 3.0 volts, about 3.5 volts, about 4.0 volts, or about 4.5 volts, or at any range derivable between any of these points.

In certain embodiments, acid is added to the solution before it is electrolyzed. The acid can be any form of acid that can provide protonation to the solution, including but not limited to hydrochloric acid. Those of ordinary skill will understand that it is possible to obtain similar chemistry and electrolysis with any number of acids or mixtures of acids. In some preferred embodiments, the acid is hydrochloric acid. In other embodiments, the amount of acid added to the solution is based on a determination of the optimum protonation rate that achieves the lowest energy to produce reactants and the highest energy to recover from products.

In still other embodiments, the electrolyzing step occurs in an electrochemical cell having a catholyte side and an anolyte side and the carbonate and/or bicarbonate products are recycled to the catholyte side of the electrochemical cell. In other embodiments, the energy required by the method is supplemented with waste-heat recovered from the gas stream.

Other embodiments of the invention comprise a method of removing carbon dioxide from a gas stream comprising: obtaining sodium hydroxide in an aqueous mixture; admixing the sodium hydroxide with the gas stream to produce sodium carbonate, sodium bicarbonate, or a mixture of sodium carbonate and bicarbonate; and separating said sodium carbonate and/or bicarbonate from the admixture, thereby removing carbon dioxide from the gas stream.

In some embodiments, the method further comprises process-controlling the method to produce substantially only sodium carbonate or substantially only sodium bicarbonate. In other embodiments, the method further comprises process-controlling the method to produce a mixture of sodium carbonate and bicarbonate, which mixture can be comprised of about X % sodium carbonate and about Y % sodium bicarbonate, with X-Y combinations being any of the following: 1-99, 2-98, 3-97, 4-96, 5-95, 6-94, 7-93, 8-92, 9-91, 10-90, 15-85, 20-80, 25-75, 30-70, 35-65, 40-60, 45-55, 50-50, 55-45, 60-40, 65-35, 70-30, 75-25, 80-20, 85-15, 90-10, 91-9, 92-8, 93-7, 94-6, 95-5, 96-4, 97-3, 98-2, or 99-1.

In certain embodiments, the admixing occurs in two separate chambers, with one chamber being used to produce sodium carbonate and the other chamber being used to produce sodium bicarbonate. In other embodiments, the admixing occurs in a bubble column or series of bubble columns In still other embodiments, separation of sodium carbonate and/or bicarbonate from the admixture involves a heated-precipitation separation process. In some embodiments, the heat for the separation process is derived from heat exchange with incoming flue-gases.

In certain embodiments, the method further comprises: transporting the sodium carbonate to a remote sequestration site; combining the carbonate products with acid in a neutralization reaction to generate pure carbon dioxide; and injecting the carbon dioxide into a carbon bank.

In some embodiments, obtaining sodium hydroxide comprises: obtaining sodium chloride; admixing the sodium chloride with water, steam, or both to produce brine; and electrolyzing the brine to produce sodium hydroxide and chlorine gas. In certain embodiments, the brine is electrolyzed using a voltage greater than or equal to about 5 volts, while in others is electrolyzed using a voltage less than about 5 volts. In some embodiments, the solution is electrolyzed using a voltage between 1 volt and 5 volts, including about 1.5 volts, about 2.0 volts, about 2.5 volts, about 3.0 volts, about 3.5 volts, about 4.0 volts, or about 4.5 volts, or at any range derivable between any of these points.

In some embodiments, acid is added to the brine before it is electrolyzed. The acid can be any form of acid that can provide protonation to the solution, including but not limited to hydrochloric acid. Those of ordinary skill will understand that it is possible to obtain similar chemistry and electrolysis with any number of acids or mixtures of acids. In some preferred embodiments, the acid is hydrochloric acid. In still other embodiments, the amount of acid added to the brine is based on a determination of the optimum protonation rate that achieves the lowest energy to produce reactants and the highest energy to recover from products.

In certain embodiments, the electrolyzing step occurs in an electrochemical cell having a catholyte side and an anolyte side and the sodium carbonate and/or bicarbonate are recycled to the catholyte side of the electrochemical cell. In other embodiments, the energy required by the method is supplemented with waste-heat recovered from the gas stream. In still other embodiments, the method further comprises collecting the chlorine gas, while in others hydrogen gas is produced. In some embodiments, the hydrogen gas and the chlorine gas are combusted to form hydrochloric acid, which is added to the brine before it is electrolyzed. In other embodiments, the hydrogen gas is combusted with atmospheric oxygen or oxygen from stock chemicals to produce water, while in others the methods comprise using the hydrogen gas to produce energy. In some embodiments, separation of sodium carbonate and/or bicarbonate from the admixture involves a heated-precipitation separation process in which the heat for the separation process is derived from the energy produced by the hydrogen gas. In others, the hydrogen gas is co-burned with coal to improve coal-fired emissions or it is used in a combustion process for fuel-cell recovery of DC electricity.

In some embodiments, the gas stream is an exhaust stream from a plant, while in others the plant is a power plant that employs a carbon-based fuel source. In certain embodiments, the exhaust stream comprises CO₂ and H₂O.

Particular embodiments of the present invention also comprise an apparatus comprising: a electrolysis chamber comprising at least one cathode and at least one anode, the chamber adapted to produce hydroxide during use; mixing equipment operably connected to the electrolysis chamber and to a conduit adapted to contain a gas stream during use, the mixing equipment adapted to admix hydroxide from the electrolysis chamber with the gas stream during use to create an admixture in which carbon, sulfur, and/or nitrogen compounds in the gas stream can react with the hydroxide; and a separation chamber operably connected to the mixing equipment and adapted to separate the admixture into a separate gas phase and solid and/or liquid phase.

In some embodiments, the electrolysis chamber comprises a membrane cell, a diaphragm, and/or mercury. In certain embodiments, the mixing equipment is a batch reactor or series of batch reactors, while in others the mixing chamber is a gas/liquid absorption/reaction device or series of gas/liquid absorption/reaction devices. In other embodiments, the mixing chamber is a crystallization tower or series of crystallization towers, while in others it is a bubble column or series of bubble columns.

In certain embodiments, the apparatus further comprises a drying chamber operably connected to the separation chamber and adapted to remove liquid from the solid and/or liquid phase during use, while in others, the drying chamber is adapted to heat the solid and/or liquid phase during use. In still other embodiments, the apparatus is further defined as operably connected to a power plant.

In some embodiments, the electrolysis chamber is adapted to produce chlorine gas and sodium hydroxide from sodium chloride and water during use. In other embodiments, the mixing equipment is adapted to admix hydroxide from the electrolysis chamber with carbon dioxide from the gas stream during use to produce carbonate and/or bicarbonate products.

In still other embodiments, the present invention comprises a method of determining optimal operating voltage and current of an electrochemical cell for low-voltage operation with respect to increased area, for a given V/I characteristic at a given protonation. In other embodiments, the invention comprises a method for determining a lower thermodynamic limit on operating voltage for a given electrolytic cell employed in the process. In certain embodiments, a method of defining ecological efficiency (∂CO₂/∂E) generally for devices that accomplish work to remove CO₂ from waste streams is provided, while other embodiments include a method of defining ecological efficiency (∂CO₂/∂E) specifically for devices that employ the present invention in any of its embodiments. Other embodiments include a method for producing extremely pure hydrogen gas at a low price-indifference point, its cost equaling the retrievable energy content.

The terms “comprise” (and any form of comprise, such as “comprises” and “comprising”), “have” (and any form of have, such as “has” and “having”), “contain” (and any form of contain, such as “contains” and “containing”), and “include” (and any form of include, such as “includes” and “including”) are open-ended linking verbs. As a result, a method or apparatus that “comprises,” “has,” “contains,” or “includes” one or more steps or elements possesses those one or more steps or elements, but is not limited to possessing only those one or more steps or elements. Likewise, an element of a device or method that “comprises,” “has,” “contains,” or “includes” one or more features possesses those one or more features, but is not limited to possessing only those one or more features. The term “using” should be interpreted in the same way. Thus, and by way of example, a step in a method that includes “using” certain information means that at least the recited information is used, but does not exclude the possibility that other, unrecited information can be used as well. Furthermore, a structure that is configured in a certain way must be configured in at least that way, but also may be configured in a way or ways that are not specified.

The terms “a” and “an” are defined as one or more than one unless this disclosure explicitly requires otherwise. The term “another” is defined as at least a second or more. The terms “substantially” and “about” are defined as at least close to (and includes) a given value or state (preferably within 10% of, more preferably within 1% of, and most preferably within 0.1% of).

As used herein, the terms “carbonates” or “carbonate products” are generally defined as mineral components containing the carbonate group, CO₃. Thus, the terms encompass both carbonate/bicarbonate mixtures and species containing solely the carbonate ion. The terms “bicarbonates” and “bicarbonate products” are generally defined as mineral components containing the bicarbonate group, HCO₃. Thus, the terms encompass both carbonate/bicarbonate mixtures and species containing solely the bicarbonate ion.

In the formation of bicarbonates and carbonates using some embodiments of the present invention, the term “ion ratio” refers to the ratio of sodium ions in the product divided by the number of carbons present in that product. Hence, a product stream formed of pure bicarbonate (NaHCO₃) may be said to have an “ion ratio” of 1.0 (Na/C), whereas a product stream formed of pure carbonate (Na₂CO₃) may be said to have an “ion ratio” of 2.0 (Na/C). By extension, an infinite number of continuous mixtures of carbonate and bicarbonate may be said to have ion ratios varying between 1.0 and 2.0.

In some preferred embodiments of the invention, hydrochloric acid is added to the sodium chloride brine feed of a chlor-alkali electrolysis cell, making the following reaction occur: H₂O+NaCl+aHCl+energy→NaOH+(½+a/2)H₂+(½+a/2)Cl₂ In this equation, the term “a” is defined as the “protonation factor” and it represents the ratio of protons (H⁺ ions) to sodium ions (Na⁺ ions).

As used herein, the term “sequestration” is used to refer generally to techniques or practices whose partial or whole effect is to remove CO₂ from point emissions sources and to store that CO₂ in some form so as to prevent its return to the atmosphere. Use of this term does not exclude any form of the described embodiments from being considered “sequestration” techniques.

As used herein, the term “ecological efficiency” is used synonymously with the term “thermodynamic efficiency” and is defined as the amount of CO₂ sequestered by certain embodiments of the present invention per energy consumed (represented by the equation “∂CO₂/∂E”). CO₂ sequestration is denominated in terms of percent of total plant CO₂; energy consumption is similarly denominated in terms of total plant power consumption.

As used herein, the terms “low-voltage electrolysis” and “LVE” are used to refer to electrolysis at voltages below about 5 volts.

Descriptions of well known processing techniques, components, and equipment are omitted so as not to unnecessarily obscure the present methods and devices in unnecessary detail. The descriptions of the present methods and devices, including those in the appendices, are exemplary and non-limiting. Certain substitutions, modifications, additions and/or rearrangements falling within the scope of the claims, but not explicitly listed in this disclosure, may become apparent to those or ordinary skill in the art based on this disclosure.

Other features and associated advantages will become apparent with reference to the following detailed description of specific embodiments in connection with the accompanying drawings.

BRIEF DESCRIPTION OF THE DRAWINGS

The following drawings illustrate by way of example and not limitation. The drawings form part of the present specification and are included to further demonstrate certain aspects of the present invention. The invention may be better understood by reference to one or more of these drawings in combination with the description of illustrative embodiments presented herein:

FIG. 1 is a process-flow diagram showing certain embodiments of the present invention.

FIG. 2A shows an apparatus for observing the primary features of one embodiment of the decarbonation portion of the present invention.

FIG. 2B shows experimental absorption/conversion results.

FIG. 2C shows experimental absorption/conversion results.

FIG. 2D is a chart showing gas/liquid contact distance (m, depth of fluid) necessary to remove 90% CO₂.

FIG. 2E is a chart showing product ion ratio vs. percent CO₂ absorbed in a test reactor.

FIG. 3 is a chart showing the thermal behavior approximated by fluid within a reaction chamber as the reaction proceeds for the time indicated.

FIG. 4 is a chart showing a flooding study of a 5′ column.

FIG. 5 is a chart showing typical voltage/current characteristic operating lines for various anolyte pH and temperature conditions.

FIG. 6 is block diagram of a system including a reactor where hydrogen is not recovered, according to embodiments of the present invention.

FIG. 7 is a block diagram of a system including a reactor where hydrogen is recovered through fuel-cell DC return, according to embodiments of the present invention.

FIG. 8 is a chart showing percent CO₂ absorption in a bubble-column vs. fluid depth vs. gas interfacial velocity at low interfacial velocities.

FIG. 9A is a chart showing the theoretical max CO₂ absorption and experimental results, according to embodiments of the present invention.

FIG. 9B shows assumptions and calculations for a flue-gas model for a plant incorporating certain embodiments of the present invention.

FIG. 9C shows the decarbonator process load and intermediate caustic requirement for a plant incorporating certain embodiments of the present invention.

FIG. 9D shows the electrolysis section load and requirements for a plant incorporating certain embodiments of the present invention.

FIG. 9E shows waste-heat calculations for a plant incorporating certain embodiments of the present invention.

FIG. 9F shows energy balance and ecological efficiency calculations for a plant incorporating certain embodiments of the present invention.

FIG. 10 shows the ecological efficiency of various modeled power plants incorporating embodiments of the present invention.

FIG. 11 is a chart showing percentage power saved for m² area of normalized LVE design.

DESCRIPTION OF ILLUSTRATIVE EMBODIMENTS

The present invention relates to sequestration processes in which carbon dioxide is removed from waste streams and converted into carbonate and/or bicarbonate products. Embodiments of the methods and apparatuses of the invention comprise one or more of the following general components: (1) an aqueous decarbonation process whereby gaseous CO₂ is absorbed into an aqueous caustic mixture and then reacted with the hydroxide to form carbonate and/or bicarbonate products; (2) a separation process whereby the carbonate and/or bicarbonate products are separated from the liquid mixture; (3) a brine electrolysis process for production of the sodium hydroxide that is used as the absorbent fluid in the decarbonation process; and (4) generation and use of by-products from the decarbonization and electrolysis processes, including chlorine gas, sodium carbonate and bicarbonate, and hydrogen gas. Each of these general components is explained in further detail below.

I. Overview of Advantages

Like any other method or apparatus that performs work to accomplish an objective, many embodiments of the present invention consume some energy to accomplish the absorption of CO₂ and other chemicals from flue-gas streams and to accomplish the other objectives of embodiments of the present invention as described herein. However, one advantage of certain embodiments of the present invention is that they provide ecologic efficiencies that are superior to those of the prior art, as explained in detail in Examples 5 and 6. As is evident from the data in Examples 5 and 6, amplified waste-heat-recovery or non-greenhouse-gas-generated energy for powering the process, use of even-lower-voltage electrolysis, and improving electrical return from hydrogen-energy-recovery can further improve the ecologic efficiency of the process, up to and surpassing the point where the process is fully powered by waste-heat recovery (and the recovery of hydrogen-energy), and absorbs virtually 100% of power-plant emitted CO₂.

Additionally, one benefit of employing the extreme chemistry of certain embodiments of the present invention such that they absorb the weak-acid CO₂ is that the process virtually completely absorbs the strong acids, SO_(X) and NO_(X), and, to a lesser extent, mercury. Tests using SO_(X)/Ar and NO_(X)/Ar in charged-load single-stage decarbonators have demonstrated 99%+ removal of these components of flue-gas (by “99%+,” it is meant that the presence of either pollutant in a 14 L/min flue-gas processing case was not detectable in the product air-stream by gas-chromatograph technique, i.e., they were effectively removed). In certain embodiments of the present invention, the incidental scrubbing of NO_(X), SO_(X), and mercury compounds can assume greater economic importance; i.e., by employing embodiments of the present invention, coals that contain large amounts of these compounds can be combusted in the power plant with, in some embodiments, less resulting pollution than with higher-grade coals processed without the benefit of the CO₂/absorption process of certain embodiments of the present invention.

Further, the scale-ability of certain embodiments of the present invention can be carried out to extreme gradations; i.e., since, in certain embodiments, the process is electrically controlled, that electrical power expense can be virtually scaled to the individual molecule of absorbent produced at any given time. Also, the ability to accurately determine the amount of CO₂ absorbed is practical and easy: weigh the carbonate/bicarbonate products formed, measure their ion ratio by assay, perform a calculation to determine moles of CO₂ absorbed, and the CO₂ absorbed is easily confirmed and measured (a factor that may benefit certain incentive regimes for the removal of CO₂ and other chemicals in flue-gas).

Another additional benefit of certain embodiments of the present invention that distinguishes them from other CO₂-removal processes is that in some market conditions, the products are worth considerably more than the reactants required or the net-power or plant-depreciation costs. In other words, certain embodiments are industrial methods of producing chlor-hydro-carbonate products at a profit, while accomplishing considerable removal of CO₂ and incidental pollutants of concern. All other competing methods are simply additional costs-of-operation.

II. Process-Flow Diagram

FIG. 1 depicts a simplified process-flow diagram illustrating general, exemplary embodiments of the apparatuses and methods of the present disclosure. This diagram is offered for illustrative purposes only, and thus it merely depicts specific embodiments of the present invention and is not intended to limit the scope of the claims in any way. As shown in FIG. 1, flue-gas (FG) enters the process at 901, potentially after initially exchanging waste-heat with a waste-heat/DC generation system. FG, entering in this example as a 300° C. mixture of gases, is first delivered by pipe 902 to FG/Bicarbonate Heat Exchanger 903, in which the FG temperature is reduced in this example to 120-140° C. Similarly, the FG continues through Anolyte/FG Heat Exchanger 904 and Catholyte Heat Exchanger 905, lowering its temperature to 95° C., and then through Water/FG Heat Exchanger 929, lowering its temperature further to 30° C. The FG exiting Water/FG Heat Exchanger 929 is then introduced to a valving arrangement, Flue-Gas Temperature Mix Control 931, in which the 30° C. FG can be mixed with 120-140° C. flue-gas, delivered also to Flue-Gas Temperature Mix Control 931 by means of Hot Flue-Gas Process Pipe 906. FG mixtures between 30-140° C. may then be differentially introduced to the bottom of Carbonation/Absorption Column 907, which can be a packed or unpacked bubble column, in which the gas is injected or sparged, with the effect that the gas forms bubbles that rise through the fluid, collecting at Upper Vent 908. In this embodiment, the partially or wholly decarbonated fluid is then injected and passed through Bicarbonation/Conversion Column 909, bubbles through the fluid in that column, is pulled by a blower further, and is ejected to Vent 910.

The fluid used in FG/Bicarbonate Heat Exchanger 903 is sodium bicarbonate/carbonate and various sulfate, nitrate, mercury, and particulates and aerosols absorbed from the flue-gas in the Absorption/Conversion Columns (907 and 909). By its contact with the 300° C. incoming FG, this liquid fluid is heated to temperatures sufficient to develop significant water vapor pressure, producing steam when the fluid is injected into Tank 911, which is then condensed in Condenser 912, with the resulting distilled water being recycled to H₂O Reclaim Tank 913, which is further used, after any needed conditioning, to form brine in Brine Mixer 914. The fluid used in the Anolyte/FG Heat Exchanger 904 is brine made from the addition of group-1 and group-2 salts (in this example NaCl) to water either supplied from Water Main Supply 915 or partially or wholly supplied from H₂O Reclaim Tank 913. This brine is protonated (acidified) by the addition of HCl in the form of HCl gas absorbed by water, or from stock chemical HCl, all controlled by pH Closed-Loop Controller 916. This fluid circulates through Anolyte Section 917 of Electrolysis Cell 933. Similarly, the fluid used in Catholyte/FG Heat Exchanger 905 is NaOH(aq) that is circulated through Catholyte Section 918 of Electrolysis Cell 933. When the pH of the Catholyte exceeds minimum pH (as proxy for concentration) value at Control Point 919, concentrated NaOH is delivered to Hydroxide Storage Tank 920.

The fluid used in Water/FG Heat Exchanger 929 is from a sufficiently large water reservoir at a sufficiently cool temperature to accomplish the heat-exchange. In some embodiments, this heat exchange system can be used as a “pre-warming” treatment for bicarbonate/carbonate solutions prior to further heat exchange in Flue-Gas/Bicarbonate Heat Exchanger 905. Also, in some embodiments, the tanking for Water Main Supply 915, H₂O HX Storage Tank 937, and H₂O Reclaim Tank 913 may be partially or wholly consolidated.

Protonated brine circulating through Anolyte Section 917 of Electrolysis Cell 933 is acted upon by the process of electrolysis, forming chlorine gas that is collected and moved through Chlorine Gas Line 921 to, in this example, Sodium Hypochlorite Reactor 924. Sodium ions and hydrogen ions (protons) are transported through the membrane of Electrolysis Cell 933 into Catholyte Section 918. Here, sodium ions displace hydrogen ions in the water, allowing the formation of hydrogen gas, which is taken away in Incoming Pure Hydrogen Gas Piping 922 to H₂/O₂ Fuel Cell 923, where it is combined with atmospheric O₂ to produce DC electricity, which is recycled to Electrolysis Cell 933 in this example, and pure water, which is recycled through Pure Water Recovery Loop 935 to H₂O Reclaim Tank 913. The chlorine gas delivered to Sodium Hypochlorite Reactor 924 is contacted (bubbled) through sodium hydroxide delivered to the reactor from Hydroxide Storage Tank 920. Sodium hypochlorite results and is tanked to market or further use as a feed-stock chemical. Some of the chlorine and HCl gas produced (using the super-stoichiometric amount, a, will produce a continuous recycle of HCl excepting make-up losses) is here combusted in HCl Fuel-cell 925, which is then recycled through HCl Acid Gas Reflux Line 926 to Brine Mixer 914.

Hydroxide produced and stored, or made from stock chemicals and tanked in Hydroxide Storage Tank 920, is the absorbent fluid introduced to Carbonation/Absorption Column 907. It is then passed through Bicarbonation/Conversion column 909 and is then delivered (as a bicarbonate/carbonate mixture in water) to FG/Bicarbonate Heat Exchanger 903. After removing water through evaporation, a product slurry of concentrated bicarbonate/carbonate is delivered to Product Bicarbonate Tank 927, where it can be drawn for further processing or refinement, or it can be sent to disposal or to market.

Each of the generalized components of the apparatuses and methods of the present disclosure as described above and shown in FIG. 1 are described in further detail below.

III. Aqueous Decarbonation (Absorption) of CO₂ from Waste Streams and its Conversion into Carbonate and Bicarbonate

As noted above, in certain embodiments, the apparatuses and methods of the present disclosure employ an aqueous decarbonation process whereby gaseous CO₂ is absorbed into an aqueous caustic mixture and then reacted with the hydroxide to form carbonate and bicarbonate products. In many embodiments of the present invention, unlike other capture/sequestration schemes, sodium hydroxide is used as the primary absorbent fluid. Sodium hydroxide, in various concentrations, is known as a ready absorber of CO₂. When carbon dioxide is brought into contact with aqueous sodium hydroxide, a continuum of products that range from pure sodium bicarbonate (NaHCO₃) to pure sodium carbonate (Na₂CO₃) can be formed, and differing conditions can be produced that will drive the equilibrium either direction, even unto completion (or its near vicinity) and in sufficient concentration (by either process chemistry or removal of water by various means) the precipitation of bicarbonate, carbonate, or a mixed precipitate containing both compounds.

When carbon dioxide is brought into contact with aqueous sodium hydroxide, the fluid within the reaction chamber approximates the behavior shown in FIG. 3 as the reaction proceeds for the time indicated. The two temperature-excursion phases correspond and identify two distinct reaction regimes:

-   -   (1) An initial absorption phase in which CO₂ is readily         absorbed. The absorption ability of the fluid declines as the OH         concentration declines, and absorption ends and in some         instances reverses when OH ion concentration is consumed. The         reaction is exothermic during this portion and forms almost         exclusively carbonate.     -   (2) A secondary conversion phase in which CO₂ is not-readily         absorbed. The passage of the flue-gas through the mixture does         not cause any net CO₂ absorption by the fluid, but the fluid is         significantly cooled by loss of heats of vaporization due to any         evaporation of water, by any loss of CO₂ to the vapor state, and         by any endothermic reactions taking place. During this phase,         sodium carbonate already formed in solution is converted to         sodium bicarbonate, by the following required net stoichiometry:         Na₂CO₃(aq)+H₂O(l)+CO₂(aq)→2NaHCO₃(aq)

This sequence of carbonation-first and then bicarbonation-second is reproducibly demonstrable by repeatedly running the apparatus in FIG. 2A (as explained in detail in Example 3) to and past the absorption limits of the fluid with different concentrations of absorbent.

The two phases are distinguished by the characteristics shown in Table 1 below.

TABLE 1 CO₂ [OH] Phase Thermodynamics Product Absorption Presence Carbonation Exothermic Na₂CO₃ Robust Plentiful Bicarbonation Endothermic NaHCO₃ Reduces, Nil De or negative minimis

While embodiments of the present invention could use the same chamber to accomplish these two processes in situ, the different natures of the reactions suggest that separating the reactions into two chambers and optimizing them separately is the proper path for preferred embodiments. Irrespective of the “internal arrangement” of transfer devices (i.e., the degree of batch-vs-continuous, few numbers of chambers, vessels, stages, etc.), the fundamental two processes occur in this sequence at molarities sufficient to provide good absorption.

Therefore, since some embodiments of the present methods and apparatuses can be process-controlled to produce pure or near-pure sodium bicarbonate, some embodiments of the present invention therefore capture one carbon per sodium produced by electrolysis, instead of ½ (an improvement in delivered ecologic efficiency nominally 2× that of carbonate production). Thus, the amount of electrolysis energy and processing spent to produce a mole of hydroxide has double the “normal” absorption power when used to form bicarbonate, compared to the absorption/energy efficiency of carbonate formation.

In various embodiments of the present invention, all forms of the bicarbonate/carbonate concentration spectrum may be produced. In preferred embodiments, the concentrations, temperatures, pressures, flow-rates, etc. of the fluids can be manipulated to optimize the proportion of “available” CO₂ absorbed to optimize the formation of bicarbonate.

Some embodiments of the invention may control pH in the absorbing fluid (OH ion concentration) as a means of controlling the absorption rate of the CO₂ and other gases. In some preferred embodiments, increased concentration of salts/carbonates can be used to further drive the reaction to bicarbonate formation. Market pricing of products and economic factors may allow operation to produce carbonate-rich product for a period of time, then bicarbonate-rich product for another period, etc., with the plant average of Na/C then forming a measure of its efficient use of the ionic species created for absorption/conversion.

By separating the two processes into two distinct chambers and transitioning between chambers at the point of OH exhaustion, temperature stasis/fall, and absorption attenuation, the manner in which a decarbonation apparatus can be built and optimized is altered. A person of skill in the art will understand that batch, pseudo-continuous, continuous, etc. versions of this simple two-stage process decarbonation process can be engineered.

Further, intending to accomplish the absorption with the least energy possible, many preferred embodiments of the invention may employ bubble-column reactors (packed or unpacked, with/without horizontal fluid flow, with or without horizontal fluid-flow) that by their nature create large liquid/gas contact area to aid mass transport, from which the overall design benefits by the freedom to utilize stages with short stage height (3 m or less) that yet achieve 90%+ absorption with little resistance or head-of-pressure to overcome in the pumping of the fluids, and therefore are designed with wide horizontal area to achieve industrial scaling (wide shallow pools or the equivalent in vessels), potentially with horizontal movement to accommodate continuous operation. Some embodiments of the invention may utilize gas-liquid contactors of many other configurations, as long as those devices attain the required gas-liquid contact.

FIG. 4 shows a flooding study of a 5′ column, in which resistance is approximately 0.01 psig, plus 1.52 psig of head to overcome the fluid-depth of 5′. These losses and other compression-costs are expected to expend less than 1% of the power plant basis, and as such are considered de minimis and not calculated in the examples. FIG. 4 confirms that extremely low resistances in the fluid-path will result in extremely low-energy compression to the effect that the ecologic efficiency of the device is not impaired by excess energy spent on compression or gas handling.

The ecological efficiency of embodiments of the present methods and apparatuses is enhanced by doing the least work possible to absorb CO₂, and one factor that detracts from that efficiency is the amount of compression, pumping of fluid and air that is required to accomplish that process. To that end, two high-efficiency absorbers (capable of removing 99% of the CO₂ from an incoming flue-gas stream that is 60% CO₂ in N₂) are designed to operate with “short stages” that achieve high CO₂ absorption rates.

Preferred embodiments of the invention use a wide-area liquid-gas transfer surface (bubble-column, packed or clear, or its equivalent in static or moving fluid vessels) to accomplish a high-absorption rate in a short height of fluid absorbent, thereby lowering the resistance necessary to bring the fluids into contact, and this “short stages design” therefore requires that wide, short “pools” or their equivalent in piping, trenches, vessels, etc. be employed to efficiently absorb large quantities of CO₂.

The decarbonation reactions of the present disclosure are generally considered by the mainstream industry and all its reference literature to be mass-transfer-limited. In practice, using packed or un-packed columns with wide-area gas-liquid contact absorption in bubble-rising-through-fluid methods, the reaction appears to have little mass-transfer limitations, or said differently, utilizing the present method of bubble-column design for liquid-gas contact appears to overcome the mass-transfer limitations handily: bubbling with zero packing through a sparger with only 30 cm of gas/liquid contact distance has been demonstrated to produce instantaneous rates of 98%+ absorption of CO₂ (see FIGS. 2B and 2C as discussed in Example 3), and over industrially-significant timeframes of 15-25 minutes the fluid retains the ability to average as much as 80%+ absorption. This is hardly seriously mass-transfer limited, and practical experimentation, even with a simple charged load run to extinction, demonstrates the ready mass-transfer of this chemisorption.

Three examples of the design of high-absorption CO₂/NaOH absorption reactors are explained in detail in Examples 1-3. The conclusions drawn from Examples 1-3 are that high-absorption rates with short stages of NaOH is proven and demonstrated as industrially capable of removing high-percentages of incoming CO₂ at low-resistance, in vessels of manufacture-able dimensions.

In summary, certain embodiments of the present invention, with respect to the decarbonation portion of the methods and apparatuses, comprise one or more of the following attributes:

-   -   (1) use of short-stages to achieve high-absorption rates of CO₂         in a carbonation phase of the reaction;     -   (2) separation and processing of carbonated fluid in a         bicarbonation process through continued contact with CO₂-bearing         process gas (or other CO₂-bearing gas with concentrations of CO₂         greater than the partial pressure of CO₂-reforming from the         absorbent fluid);     -   (3) possession of a process sequence that can be used, by         process control of state variables and concentration, to produce         pure bicarbonate, pure carbonate, and all various mixtures         between; and     -   (4) embodiments of the invention can be as efficient as a 1:1         sodium/carbon absorption ratio; this optimizes the CO₂ absorbed         per kw-hr (a variant of Ecologic Efficiency, (∂CO₂/∂E), used in         producing the reactant.         IV. Separation of Products

As noted above, in certain embodiments, the apparatuses and methods of the present disclosure employ a separation process by which the carbonate and bicarbonate products are separated from the liquid solution. Separation of liquid solution products requires an involved process. The formation of sodium hydrogen carbonate (NaHCO₃ or sodium bicarbonate) and sodium carbonate (Na₂CO₃ or soda ash) in a liquid equilibrium with sodium hydroxide (NaOH or caustic soda) occurs over a wide range of temperatures and pressures and provides different end-points of the equilibrium given different partial pressures of CO₂. By manipulating the basic concentration, temperature, pressure, reactor size, fluid depth, and degree of carbonation, precipitates of carbonate and bicarbonate may be caused to occur. Alternatively, carbonate/bicarbonate products may be separated from their water by the exchange of heat with incoming flue-gases, in some preferred embodiments. Further, due to the solubility product constant differences between sodium carbonate and sodium bicarbonate, certain non-intuitive processing points can be reached; e.g., one of the peculiarities of the equilibria of carbonates of sodium in certain caustic solutions is that the addition of heat encourages precipitation of solid; also, at certain conditions, carbonates have been demonstrated to self-precipitate from the aqueous solution at high (93%+) purity.

Alternatively, in certain embodiments the heat for the separation process may be derived from the hydrogen produced in the original electrolysis or from creative uses of the waste-heat contained in the incoming flue-gas stream. The crystallization process inherently purifies the crystallizing mineral through the well-known process of purification by crystallization.

The exit liquid streams, depending upon reactor design, may include water, NaOH, NaHCO₃, Na₂CO₃, and other dissolved gases in various equilibria. Dissolved trace emission components such as H₂SO₄, HNO₃, and Hg may also be found. In one embodiment, to separate/remove the exiting liquid streams, e.g., removing/separating the water from the carbonates (in this sense of the word, “carbonates” means mixtures of carbonate and bicarbonate, potentially with hydroxides present as well; any separation technique applied to any such mixture would likely include adding heat energy to evaporate water from the mixture), the water may be boiled causing the water to be evaporated using Reboiler 106, shown in FIG. 6. Alternatively, retaining a partial basic solution (e.g., NaOH at approximately 1 molal) and subsequently heating the solution in a separating chamber may cause the relatively pure Na₂CO₃ to precipitate into a holding tank and the remaining NaOH re-circulates back to Reactor 200. In other embodiments, pure carbonate, pure bicarbonate, and mixtures of the two in equilibrium concentrations and/or in a slurry or concentrated form may then be periodically transported to a truck/tank-car. In other embodiments, the liquid streams may be displaced to evaporation tanks/fields, where the liquid, such as water, may be carried off by evaporation.

Referring to FIG. 6, the reactor design shown may recover the energy stored in the electrolyzed hydrogen either as a combustion fuel, a boiler gas, or in H₂/O₂ fuel cells. Reactor 200 may be employed to produce a steady-state operation where NaOH and NaHCO₃ may by produced in approximately 50:50 proportions. The hydrogen gas produced in the original electrolysis may be used to provide heat, and the NaHCO₃ may be precipitated in Separation Chamber 108 with the remaining NaOH refluxed to Reactor 200. The slurry from Separation Chamber 108 may be provided to Water Treatment Chamber 110, which may be coupled to Separation Chamber 108. Alternatively, the slurry may be stored and subsequently provided to Water Treatment Chamber 110 as needed.

FIG. 7 illustrates another reactor design, according to an embodiment of the present invention. In particular, FIG. 7 shows a re-capturing of some excess energy used to create the hydrogen by-product. The use of a tandem, on-site high-efficiency fuel-cell may allow for a direct-current recovery that may be used to supplement and partially supply the electrolysis current. Mixing Chamber 300 provides an admixture including, but not limited to, a percentage of NaOH, NaHCO₃, and NO_(X), SO_(X), and Hg to Separation Chamber 308. Separation Chamber 308 may separate the admixture into solid and/or liquid phases by a providing heat to the admixture. A drying chamber (not shown) of Separation Chamber 308 may remove the liquids from the solid and/or liquid phase during the process by providing the heat. A resulting dilute form of NaOH is provided to Boiler 306 which boils the diluted NaOH into a concentrated form and provides the concentrate to Mixing Chamber 300 via a reflux loop. The water from Boiler 306 can be provided to Electrolysis Chamber 302, in particular Brine Mixer 302A. The resultant Na₂CO₃/NaHCO₃ (slurry) from Separation Chamber 308 can be provided for commercial use. In one embodiment, the carbonate slurry can be directly or indirectly (e.g., storing the NaHCO₃ for later use in process such as hard-water treatment) provided to a Water Treatment Plant 310. Alternatively, the NaHCO₃ can be further refined, dried, shipped, and provided for other industrial uses.

The release of gaseous products includes a concern whether NaOH or components of same can be released safely, i.e., emitting “basic rain” from a power-plant is equally to be avoided with emitting “acid rain.” However, sodium hydroxide is normally used as a scrubbing element in power-plant production and is approved for use by the EPA. The handling of sodium hydroxide in power plants as well as the procedures to avoid basic release is well-known in the art. For example, a simple and inexpensive condenser/reflux unit may prevent any significant emission of NaOH in gaseous exhaust.

In a carbonate separation precipitation method according to certain embodiments of the present invention, the carbonate equilibrium sterically binds carbon-dioxide and absorbs the gas on contact, with a substantially instantaneous conversion to carbonate ion. The reaction chain may be mass-transport limited such that once the carbon-dioxide has been absorbed by the base, the subsequent ionic reactions occur at rapid pace.

The sodium carbonate equilibrium has a characteristic where as temperature is raised, Na₂CO₃ naturally precipitates and collects, which makes it amenable to be withdrawn as a slurry, with some fractional NaOH drawn off in the slurry. In one embodiment, a bleed-through treatment of this slurry with some of the wet chlorine produced in the chlorine cycle may be used to reduce the NaOH to trace NaCl in the NaHCO₃ at levels that either approximate, or are less than, sodium carbonate produced by mining subterranean “trona” or deposits. As such, the sodium carbonate/caustic equilibria provides carbon with complete transport from gas to liquid to solid. In other embodiments, it may be beneficial to use the carbonate loop as a collection medium to collect a slurry of ash, sodium hydroxide, and other various carbonates and impurities and truck off the slurry as road-base.

V. Brine Electrolysis for the Production of Absorbent Fluid At Low Energies

As noted above, in certain embodiments, the apparatuses and methods of the present disclosure employ brine electrolysis for production of the sodium hydroxide that is used as the absorbent fluid in the decarbonation process. Brine electrolysis is an electrochemical process primarily used in the production of concentrated sodium hydroxide (caustic soda) and chlorine gas, and is typically described throughout the relevant literature by the following equation: 2NaCl+2H₂O+e−→2NaOH+H₂(g)+Cl₂(g)

Brine electrolysis may be accomplished by three general types of standard electrolysis cells: diaphragm, mercury, and membrane cells. Each of these types of cells produces the same output products from the same input reactants. They differ from each other primarily in the way the reactants and products are separated from each other.

In one embodiment, a membrane cell may be used due to several factors. First, environmental concerns over mercury have reduced the demand for the mercury cell. Second, the diaphragm cells may produce a relatively weak caustic product which contains significant concentrations of salt and chloride ion and requires considerable subsequent reprocessing/separation to remove the significant salt content from the caustic. Third, improvements in fluorinated polymer technology have increased the life-time and electrical efficiency of membrane cell technology, where lifetimes in excess of 5 years are routinely guaranteed in the industrial markets. Further, the power-per-ton-of-caustic efficiencies exceeds those of both diaphragm and mercury cells in preferred implementations.

Membrane cell processing units are typified, but not limited to, the following generalized inputs and outputs: Anode: 26% NaCl input+2275 kwh/ton Cl₂→Cl₂(g)+24% NaOH Cathode: H₂O input+e−→30-33% NaOH+H₂(g)

It is noted that the power requirements (e.g., 2275 kwh/ton of chlorine) may depend upon individual electrolysis cell designs. As such, the requirements may vary.

Many preferred embodiments may employ membrane cells in this function. Membrane cells have several advantages over other brine-electrolysis processes. First, membrane cells neither contain nor produce any environmentally sensitive emissions (e.g., mercury) and are electrically efficient when compared with diaphragm and mercury cells. They also employ a concentrated/dilute/make-up NaCl loop such that they may be well-suited for use as a continuous “salt loop” processing unit. Next, NaOH produced in membrane cells without further evaporation/concentration may be a naturally appropriate level of concentration for use in a decarbonation process (e.g., 30-33% NaOH by weight). Further, hydrogen produced by membrane cells is “clean,” approximately “electronic grade,” and relatively clear of NaCl or other contamination. As such, hydrogen may be compressed and tanked off as electronic-grade H₂ gas, used for power-production on-site such as combustion mix with low-grade coal or for combustion-technology gains. Alternatively, the hydrogen may be used for a boiler fuel for the separation processes, which may occur after decarbonation. Membrane cell technology may also be easily scaled from laboratory to plant-size production by the addition of small incremental units. Additionally, chlorine gas produced by the membrane process is less “wet” than that produced by other standard electrolytic processes. As such, a one-stage compression cycle may be sufficient for production of water-treatment grade chlorine.

The above represents the published and practiced state of the art as normally accomplished toward the end of producing commercial chlorine gas and caustic soda. However, the aims of certain embodiments of the present invention are different in several respects, which leads to different chemical techniques being employed to accomplish the differing ends of certain embodiments of the present invention.

A. Use of Low-Voltage Electrolysis Techniques

In some embodiments of the present invention, the brine electrolysis incorporates low-voltage electrolysis (LVE) techniques, thereby improving the thermodynamic efficiency of the process. Certain embodiments of the present invention do not exclusively manufacture caustic soda as an end-product, but instead use NaOH primarily as an intermediate absorbent to absorb CO₂ from flue-gas prior to its exit to the environment. Because the chlor-alkali business generally involves shipping caustic soda from the manufacturing plant to its point-of-use, transporting large quantities of water in the caustic soda is uneconomic, so caustic is generally concentrated to approximately 55 wt % for shipping as a liquid by the energy-intensive removal of water by steam-evaporation, and in some cases, it is concentrated to an anhydrous solid, generally pelletized form. This concentration is achieved most generally by running electrolysis cells at voltages over 5V (in the parlance, “at significant over-voltage”), which achieves the above-mentioned 30-35% NaOH, which is then followed by a steam-evaporation cycle to achieve the 55% (or to completely dry the product to anhydrous, palletized states, etc.).

Most embodiments of the present invention do not transport NaOH as a product, and it is producible at usable concentrations (as an aqueous absorbent fluid) at voltages significantly below the 5V+ standards used in chlor-alkali plant operation. The impact of employing LVE on the thermodynamic efficiency of the present invention cannot be over-estimated, since power consumed is exactly to the simple DC equation: P=V(voltage)×I(current)×(current Efficiency)

Because the current is fixed by the electrochemical process (one pair of electrons for each molecule, etc.), the power is nearly entirely regulated by the voltage required to electrolyze (an additional strong factor is the current efficiency, which is also a function of applied voltage). Since embodiments of the present invention employ LVE with voltages easily demonstrated in standard electrolysis cells, by alteration of operating conditions, as low as 2.1V, through process and geometric modifications to a standard electrochemical membrane cell, embodiments of the present invention consume less power (kw-hr) for each amount of NaOH formed than traditional high-voltage chlor-alkali electrolysis. For these reasons, preferred embodiments of the present invention include electrolysis units that are designed to employ all available techniques to accomplish low-voltage operation, including, but not limited to: narrow-gap operation, higher-pressure, wide-area membranes, altered concentrations of anolyte and catholyte and protonation-ion ratios. Further aspects of LVE are explained in detail in Example 4.

B. “Point of Indifference” Hydrogen Use

Typical chlor-alkali operation produces hydrogen gas that is either burned on site as boiler-fuel for steam-evaporation (see above), or in many cases, is suppressed entirely by the use of an air-electrode; e.g., a device that blows air containing oxygen on the cathode causing the immediate reduction reaction to occur: H₂(g)+½O₂(g)→H₂O(l/g), which alters the electrochemical summation of energies and lowers the voltage necessary to produce caustic and chlorine (in some cases as low as 2.8V in various industry literature) at the expense of not producing hydrogen. A benefit to preferred embodiments of the present invention is that they have no need for hydrogen as a steam-evaporation boiler fuel.

Some embodiments of the present invention may include an “air-electrode” process that suppresses hydrogen production (and zeroes the ability to recover energy from that hydrogen), but many preferred embodiments utilize the production of hydrogen for either energy return or for use as a chemical feed-stock for other processes.

Plants employing certain embodiments of the present invention therefore have a “point of indifference” regarding the use of hydrogen so produced; i.e., the plant produces hydrogen for its energy return (e.g., 60% of its energy content in an example case, for instance), and that amount of energy has a certain economic value, and instead of using the hydrogen for energy return, the hydrogen may be traded or sold for amounts in excess or equal to that economic value of the energy alone. In this manner, plants of this type represent “hydrogen wells” of a sort. Hydrogen is produced and consumed for its electric value, and anyone desiring the hydrogen for other purposes need only trade that electric value or its economic equivalent to maintain the economics of the process. This embodiment has beneficial implications for future “hydrogen economy” schemes: having a ready source of hydrogen, available at a price-indifference cost point lower than its innate energy content, may prove a useful and advantageous feature of this technology.

C. Use of Protonated Brine Optimization Techniques

Certain embodiments of the present invention intentionally optimize the production of hydrogen instead of suppressing it, by the following means of Protonated Brine Optimization. The general chlor-alkali industry has, in some occasions, employed the addition of HCl in the form of hydrochloric acid to the brine (NaCl) cell called the anolyte chamber. This “protonation” of the brine has the effect of lowering the voltage required to produce a specified amount of caustic in that it lowers the power required to make the reactant/absorbent of certain embodiments of the present invention. In the normal body of work of chlor-alkali plants, the cause of this voltage-lowering effect is attributed to “neutralizing NaOH that returns across the membrane,” a process that has been studied versus membrane selectivity, etc. and is well-understood. Generally speaking, this “neutralization” is seen to produce only salt water [NaOH (returning)+HCl (anolyte)→NaCl+H₂O] and is not shown to alter the stoichiometry of the products. However, one point that is not well-understood or exploited in the art is that the addition of HCl fundamentally does indeed alter the stoichiometry of the equation thus: NaCl+aHCl+H₂O→NaOH+(½+a/2)H₂+(½+a/2)Cl₂

This additional quantity of hydrogen and chlorine produced is particularly of interest to the present invention, as embodiments of the present invention rely upon energy-recovery from hydrogen (which is enhanced when more hydrogen is produced and is more economic when more chlorine gas is produced, per mole of absorbent NaOH manufactured). That this additional bounty of hydrogen-for-energy-recovery and chlorine-for-sale is produced while the overall electrical voltage (therefore power and cost) is reduced leads certain embodiments of the present invention to optimize the value “a” for the lowest energy to produce reactants and the highest energy to recover from products. The optimum generally lies between 0.5 and 1.0M HCl in the solution of NaCl(aq). However, the optimization is specific for each cell design, geometry, concentration, temperature, and pressure regime. However, for each electrochemical cell, there is an optimum protonation rate (“a”) that achieves a lowest-energy operation. In practice, extremely high “a” values (>0.15M at 90° C. for instance) will possibly blister most commercially-available membranes in short order. Of course, while HCl is a preferred acid for protonation of brine in the invention, many other acids, as known to those of skill in the art, can be used to protonate the brine.

D. Self-Producing the HCl that is Used for Protonation

Because certain embodiments of the present invention both use input HCl and produce H₂ and Cl₂ gas, the protonation of brine can be made self-reciprocating; i.e., H₂ and Cl₂ product gases can be burnt (in efficient fuel-cells or in plain burners) to produce HCl gas, which can then be recycled to the anolyte for protonation of the brine. The energy recovered from H₂/Cl₂ combustion is higher than that recovered from H₂/O₂ combustion. This adds to the thermodynamic efficiency of the invention.

Some preferred embodiments of the present invention use an absorption/conversion/regeneration pathway as a “front-end concentration/absorption process” that is then used to absorb and concentrate CO₂ for use in geologic, oceanic, or terrestrial sequestration techniques (for example, those that inject CO₂ into carbon banks) by the following means or similar:

-   -   (1) All hydrogen is combusted to produce HCl gas.     -   (2) All HCl gas is reacted with the sodium bicarbonate so         produced     -   (3) Through the associated neutralization reaction, nearly 100%         pure CO₂ is released, and salt water is regenerated that can be         recycled for further absorption cycles.     -   (4) By this process, the invention is used to absorb, convert,         and then release the CO₂, with the net effect that the gas is         removed from the flue-stream, and concentrated for further         sequestration techniques to then process.

E. Mixing Carbonates and Bicarbonates Back into the Catholytic Fluids

Unlike the chlor-alkali industrial use of chlorine/hydrogen cells, some embodiments of the present invention also recycle carbonate and bicarbonate mixtures to the catholyte (caustic) side of the electrochemical cell. Such techniques are wide and varied, but each operating point for the entire process has an optimum recycle of bi/carbonate mixtures to the catholyte, as this can, in some concentrations and conditions, lower cell voltage, and therefore cell power.

F. Use of Waste-Heat-Recovery for Heating of Fluids

Because certain embodiments of the present invention are employed in the presence of a power-plant or large emission of CO₂ in the form of flue-gas or other hot gases from combustion, there is ample opportunity for heat-exchange, unlike standard chlor-alkali processes. For instance, a typical incoming flue-gas temperature (after electro-static precipitation treatment, for instance) might well be 300° C. Cooling that flue-gas to a point less than 300° C., while warming the anolyte and catholyte fluids (which, for LVE, should generally be retained >90° C.) allows certain embodiments of the present invention to operate without the power-losses associated with anolyte and catholyte heaters.

G. Use of Waste-Heat-Recovery for Powering Process Equipment

Generally, since the flue-gas that is available at power-plant exits at temperatures between 100° C. (scrubbed typical), 300° C. (after precipitation processing), and 900° C. (precipitation entrance), or other such figures, considerable waste-heat processing can be extracted by cooling the incoming flue-gas through heat-exchange with a power-recovery cycle, of which an example is an ammonia-water cycle (“Kalina” patent process, for example), a steam cycle, or any such cycle that accomplishes the same thermodynamic means. Since certain embodiments of the present invention rely upon DC power to accomplish the manufacture of the reagent/absorbent for the present invention, the process can be directly powered, partially or wholly, by waste-heat recovery that is accomplished without the normal transformer losses associated with converting that DC power to AC power for other uses. Further, through the use of waste-heat-to-work engines, significant efficiencies can be accomplished without an electricity generation step being employed at all. In some conditions, these waste-heat recovery energy quantities may be found to entirely power embodiments of the present invention.

VI. Generation and Use of By-Products from the Decarbonization and Electrolysis Processes

As noted above, certain embodiments of the apparatuses and methods of the present disclosure produce a number of useful by-products from the decarbonization and electrolysis processes, including chlorine gas, sodium bicarbonate, and hydrogen gas. In some embodiments, the hydrogen gas produced by the embodiments of the present invention is incorporated into a hydrogen energy recapture loop. In one embodiment, the present invention may include current fluorinated polymer membrane technologies to reduce chlorine-ion migration for the decarbonization process. The process may therefore function without extensive energy and cost expenditure to separate out the chlorine ion; the decarbonation and separation loops are relatively chloride-free. As such, an embodiment of a decarbonation reactor of the present invention may use common salt, water, and carbon dioxide exhaust combined with electricity to form chlorine gas, sodium bicarbonate, and power-recovery through hydrogen combustion as follows: 2NaCl+H₂O+2CO₂ +e−→2NaHCO₃+Cl₂+[½H₂+atm O₂ →e−]

A. Hydrogen Energy Recapture Loop

Two techniques have developed that may use the hydrogen energy captured by embodiments of the present invention. The first is co-burning of hydrogen with coal to improve coal-fired emissions, and the second technique involves hydrogen/oxygen fuel cell recovery of DC electricity. Approximately 22% to 32% of the electrolysis-spent energy may be recovered by the H₂/O₂ combustion. Alternatively, H₂ and Cl₂ may combust into Cl₂ and HCl directly or through fuel-cell or DC recovery. Sources of heat from waste-heat removal, from either the electrolysis reaction, which produces approximately 135° C. caustic soda to tank, or from the decarbonation process itself, which absorbs various heats-of-solution, heats-of-vaporization, and heat liberated in the exothermic reaction, can be utilized by well-known techniques (i.e., re-boilers, etc.) at power plant locations for the pre-heating of combustion gases or other uses.

In one embodiment, commercial fuel-cell production of DC electricity may be advantageous due to the easy-to-handle and safe operations at sub-atmospheric pressures. Immediate consumption of the produced hydrogen may also directly reduce the electrical load cost for the brine electrolysis. Further, since the hydrogen-energy recovery cycle may be produced with off-peak electrical production of H₂, Cl₂, and NaOH, where H₂ may be subsequently used to provide electricity during on-peak loads, the present disclosure provides for making reactants at low-cost while subsequently producing auxiliary high-cost on-peak electricity and simultaneously performing a decarbonation process. The economic utility of an H₂ energy recovery cycle to increase the peak power production of a plant by augmenting the current production with H₂ combustion capacity as either fuel or in a fuel cell may provide for the utility of a self-consumption basis.

Alternatively, given a clean carbon-produced source of electronic grade hydrogen gas, municipal utilities, industrial companies, and power-generation facilities may prosper from using hydrogen produced in municipal bus fleets, trains, and other public or private uses of hydrogen fuel.

B. Other Uses of By-Products from the Decarbonization Process

In one embodiment, the chlorine gas may be a primary oxidizing reagent used to kill bacteria in water-treatment plants around the world. Chlorine, and the some 100+ derivative feed-stock chemicals that derive from it, are often cited as being incorporated in as much as 30%+ of US domestic GDP. It may also be used in the manufacturing of the largest industrial chemical, hydrochloric acid. Chlorine is also extensively used in the plastics industry as its most common non-carbon reactant.

Sodium carbonate is a by-product of the process described in the present invention that is commonly used in the production of soap, detergents, and shampoos world-wide, as well as a flux in the manufacture of glass. Further, power utilities, as well as private homes, utilize sodium bicarbonate to soften hard water by the following general reaction: CaCl₂(aq)+NaHCO₃(aq)→CaCO₃(precipitate)+NaCl(aq)+HCl(aq)

A similar process may be employed using sodium carbonates and bicarbonates from this process to perform ion-exchanges with multiple group 1 and group 2 salts to precipitate various carbonates.

Another example of the by-products produced from the decarbonation process is hydrogen gas. Hydrogen gas, in electronic grade, is a high-form of energy carrier. Conversely, the hydrogen fuel produced can be burned with “dirtier” levels of coal to reduce that fuel's emissions, can be burned as boiler feed in the separation process, or can be utilized in hydrogen-vehicle fleets.

In further embodiments, it is possible to accomplish the effect of transporting carbon dioxide to remote sequestration sites by the following method, or its equivalent:

-   -   (1) At the power-plant site, CO₂ and other pollutants are         absorbed by the process or any of its variants, along with the         production of hydrogen, chlorine, and carbonates.     -   (2) At the remote sequestration site, hydrochloric acid and         carbonates, are again combined in a neutralization reaction that         generates virtually pure CO₂. CO₂ produced by these means may         then be injected into the carbon bank.

By these means, the same net effect of transporting CO₂ between the power site and the sequestration site is achieved without the physical transport of CO₂ by liquification and transport by pipe-line, trucking, etc.

EXAMPLES

The following examples are included to demonstrate preferred embodiments of the invention. These embodiments provide a feasible economic solution to reduce or even substantially eliminate the carbon dioxide and other pollutants from power plants by providing and using the resulting reactants in commercial or industrial processes and/or by recycling energy.

It should be appreciated by those of skill in the art that the techniques disclosed in the examples which follow represent techniques discovered by the inventor to function well in the practice of the invention, and thus can be considered to constitute preferred modes for its practice. However, those of skill in the art should, in light of the present disclosure, appreciate that many changes can be made in the specific embodiments which are disclosed and still obtain a like or similar result without departing from the spirit and scope of the invention.

Example 1 CO₂/NaOH Bubble Column Reactor Design by Graphical Methods

In the bubble-column reactor designed for this example, there are four primary flow streams, namely:

-   -   (1) Liquid flowing into the fluid of the bubble column at a         given volumetric flow-rate (V1=cubic volume of fluid per time);         in the chosen case, the incoming volumetric flow-rate equals the         outgoing volumetric flow rate. Hence, both are V1). In this         example, V1=0.001 m³/sec.     -   (2) Vg0=the incoming volumetric flow rate of gas, which will be         partially or wholly absorbed by the absorbent fluid. In this         example, Vg0=0.05 m³/sec.     -   (3) Vg=the exiting volumetric flow-rate of gas. In this example,         Vg=0.02 m³/sec.

A bubble-column reactor was designed as bound by the above conditions. Sixty-percent incoming CO₂ in a flue-gas was to be removed by bubbling through a solution of concentrated sodium hydroxide. The reaction is mass-transfer limited. The objective of the example was to calculate the reactor size (height and diameter) necessary to remove 99.9% of the carbon dioxide. P=2 atm, T=298K. Using the graphical data available in FIG. 8, this example describes the design of both a tall reactor (2.36 m) and a short reactor (0.41 m). FIG. 8 is a chart showing percent CO₂ absorption of CO₂ in a bubble-column vs. fluid depth vs. gas interfacial velocity at low interfacial velocities (Schumpe et al., 1979).

2.36 m Height Column Solution

The conversion approaches 100% at a superficial velocity (Ug0) of approximately 0.04 m/s. This velocity is in the bubbly-flow range (in water-like solutions this is approximately 0.05 m/s). Knowing the volumetric gas flow requirement (Vg0), the diameter of the column was calculated: Ac=Vg0/Ug0=0.05/0.04=1.25 m2 Dc=2√{square root over (Ac/π)}=√{square root over (1.25/π)}=1.26 m

Therefore, a conversion of 99% of the incoming 60% CO₂ requires a column of 2.36 m height, 1.25 m² area, having a diameter of 1.26 m, and a total volume of 2.95 m³.

0.41 m Height Column Solution

Conversion in a 0.41 m tall column requires a superficial gas velocity of about 0.02 m/s. Similar to above: Ac=Vg0/Ug0=0.05/0.02=2.50 m2 Dc=2√{square root over (Ac/π)}=2√{square root over (2.5/π)}=1.78 m

Therefore, a conversion of 99% of the incoming 60% CO₂ requires a column of 0.41 m height, 2.50 m² area, having a diameter of 1.78 m, and a total volume of 1.03 m³.

In summary, it is demonstrated through this example that shorter columns are more efficient on a per-volume basis in stripping carbon dioxide from a flue gas; for this example, by a factor of 3. Therefore, for preferred embodiments of the present invention, the design targets short stages and/or multiple-stage reactors composed of short stages.

Example 2 CO₂/NaOH Bubble-Column Design by Mass-Transfer Coefficient Solution

The objective of this example was to determine the mass-transfer coefficient, kla (moles/sec/volume), from theoretical build-up. It was determined from this example that this correlative method can potentially lead to inconclusive results; i.e., this example highlights the difficulty in predicting actual results from theory due to the indeterminacy of measuring some of the critical parameters. Therefore, only experimental scaling can conclusively determine the result of a large decarbonation unit.

The following equations for gas-hold-up (εg) and mole-transfer (kLa) are from correlations from Akita and Yoshida (1973), and are valid for carbon dioxide and water systems at relatively large column heights and diameters (i.e., >0.1 m):

Gas-Hold-Up $\frac{ɛ\; g}{\left( {1 - {ɛ\; g}} \right)4} = \begin{matrix} {C*\left\lbrack {g*{Dc}\; 2*\rho\;{L/\sigma}} \right\rbrack{1/8}*} \\ {\left\lbrack {g*{Dc}\;{2/{vl}}\; 2} \right\rbrack{1/12}*} \\ \left\lbrack {\mu\;{g/\sqrt{g}}*{Dc}} \right\rbrack \end{matrix}$ and Mass-Transfer  Coefficient ${{kLa}\left( {1/\sec} \right)} = \begin{matrix} \begin{matrix} {\left\lbrack {{{Cco}\; 2*{Dco}\; 2} - {h\;{20/{Dc}}\; 2}} \right\rbrack*} \\ {\left\lbrack {{{{vL}/{Dco}}\; 2} - {h\; 20}} \right\rbrack 0.2*} \end{matrix} \\ {\left\lbrack {g*{Dc}\; 2*\rho\;{L/\sigma}} \right\rbrack 0.62*} \\ {\left\lbrack {g*{Dc}\;{3/{vl}}\; 2} \right\rbrack*ɛ\; 11} \end{matrix}$

Where

-   -   εg=gas hold-up factor     -   Cco2=concentration of CO₂ in flue-gas     -   Dc=diameter of column     -   νL=0.0001 m2/sec     -   σ=1 cP=0.1 Pa*sec     -   ρL=998 kg/m3         and since         Dco2−h20P=1.661 m2*Pa/sec,         therefore,         Dco2−HO=1.661/5.067*10(5)=3.278*10(−6)m2/sec

The driving force is the difference between the equilibrium concentration of carbon dioxide (Cco2*) and the actual liquid phase concentration of carbon dioxide (Cco2), which this example assumes is zero; i.e., the sodium hydroxide present instantaneously neutralizes the aqueous carbon dioxide “acid.” The rate of mole transfer per reactor volume can therefore be written as: Nco2=kLa*[Cco2*−Cco2]=kLa(Cco2*) Rate of Mole Transfer Needed to Remove 99.99% of the carbon dioxide in the flue-gas. CO₂ is assumed to be an ideal gas under the conditions of the column.

Cubic volume/sec: Vg0=0.05 m3/sec∴Vco2=0.6*Vg0=0.03 m3/s

Mole/Sec: Vco2*P/RT=[0.03 M3/sec*5 Atm]/[0.082 m3 atm/kmolK*298]*1000 gmmole/1 kmole=6.14 mole/sec Nco2(mole/sec)=0.999(moleCO2removed/molesCO2in)*6.14 mole/sec=6.13 mole/sec

Other Fluid Properties Necessary for Model Correlation

Setting the initial superficial velocity at the bubbly flow limit (Vg0=0.05 m/s), the area and diameter of the column was calculated: Ac=Vg0/UgO=0.05/0.05=1.0 m2 Dc=2√{square root over (Ac/π)}=2√{square root over (1.0/π)}=1.13 m

For the gas-phase hold-up reactions this example sets C=0.2 and assumes that the superficial velocity (Ug) is the average of the entering and exiting velocities; Ug=0.035 m/s=average (0.05 m/s, 0.02 m/s), and using an equation solver, it was found that εg=0.055.

Next, the mole transfer rate constant was solved for:

$\begin{matrix} {{{kLa}\left( {1/\sec} \right)} = {\frac{{0.6*3.278*10} - {6\mspace{14mu} m\;{2/\sec}}}{\left\lbrack {0.6\mspace{14mu} m} \right\rbrack 2}*}} \\ {\frac{0.0001\mspace{14mu} m\;{2/\sec}}{{3.278 \times 10} - {6\mspace{14mu} m\;{2/\sec}}}*} \\ {\left\lbrack \frac{9.8\mspace{14mu}{m/s}\; 2*\left( {0.6\mspace{14mu} m} \right)2*998\mspace{14mu}{{kg}/m}\; 3}{0.0696\mspace{14mu}{{kg}/\sec}\; 2} \right\rbrack*} \\ {\left\lbrack \frac{\left( {9.8\mspace{14mu}{m/\sec}\; 2} \right)*\left( {0.6\mspace{14mu} m} \right)3}{\left\lbrack {0.0001\mspace{14mu} m\;{2/\sec}} \right\rbrack 2} \right\rbrack*(0.055)1.1} \\ {= {0.386/\sec}} \end{matrix}$ kLa = 0.386/sec  Going back to the driving force equation, the reactor volume (V) was solved for: V=Nco2/[(kLa)(Cco2*)]=6.13 mole/sec/(0.386/sec*(103.6 mole/m3))=0.15 m3 and Hc=0.15 m3/1 m2=0.15M

Therefore, the dimensions of a bubble column are Dc=1.13 m and Hc=0.15 m, resulting in a significant difference from actual results in real bubble columns

Several assumptions can explain the difference in the correlative models (that are considered the best models of this behavior) and the actual results:

-   -   (1) The sodium hydroxide was assumed to have the properties of         water (density, surface tension, etc.); and     -   (2) The concentration of CO₂ in the solution might not be well         characterized as zero; this is the more likely operand; e.g., if         the CO₂ effective concentration is not zero, then the driving         force is less, and a taller column is needed.

It should also be noted that this theoretical correlation suffers under a condition that is also its strength: because terms such as (νL=0.0001 m2/sec) are often squared in the denominator, small variations in these numbers produce gigantic effects. This type of theoretical build-up is good for curve-fitting ex-post-facto, but is not a good predictor of mass-transfer for design purposes. Further, there are striking fluid-flow effects on the absorption/conversion rate of CO₂, such that designs at-differing-and-progressive scales are indicated.

Example 3 CO₂/NaOH Bubble-Column Design (depth) from Experimental Data

Note that the reliance of certain embodiments of the present invention upon the “short stage efficiency theory” described herein (3 m or less gas-liquid contact distance, or fluid stage height, to achieve >90% absorption) is confirmed by two different calculation techniques that are consistent with practiced chemical engineering design. However, in certain cases (as noted above) certain simplifying assumptions have been made in these design calculations, so experimental verification was indicated and performed with the Results displayed in FIGS. 2B and 2C (explained in further detail below).

Each of these processing runs obtained a certain CO₂ absorption over a certain gas-liquid contact distance (namely the height of the fluid in unpacked, open bubble-column cases); e.g., 20% absorption through 30 cm of fluid.

If the gas were then passed through a second column of the same design and state-of-conditions, the same absorption would occur again; i.e., 20% of the remaining 80% of initial CO₂ would again be absorbed. This relationship eventually attenuates; however, given the highly absorptive characteristics of the absorbent fluid, and the tendency of the chemisorption to persist with robust absorption even of dilute CO₂ in the flue-gas, this effect is ignored for this example and a design of 90% removal is effected.

One can see that further passes of the fluid through the absorption fluid would again reduce remaining CO₂ by 20%, etc. until sufficient passes have been accomplished to attain the desired absorption level (in this case 90%).

This results in a “number of base stages” design that determines the depth of fluid (in multiple depths of stages of 30 cm height) that is required to attain 90%. Assuming each stage absorbs the same % CO₂/distance as the former, the results in FIGS. 2B and 2C were obtained and are graphically represented in FIGS. 2D and 2E.

FIG. 2A shows an apparatus for observing the primary features of one embodiment of the decarbonation portion of the present invention. The apparatus in FIG. 2A (or one with similar effect) can be operated according to the procedure listed below:

-   -   (1) Carbonation Unit 801 is charged with NaOH with a test load         (for example, 1M NaOH in 25° C. water) to a depth of 30 cm,         packed or unpacked.     -   (2) Flue-gas, simulated or actual, in this case, for a typical         coal-fired flue-gas exhaust (16% CO₂, 84% N₂, SO_(X)/NO_(X)<1%         or in natural ppm rates) is introduced to Carbonation Unit 801,         effectively sparged in an unpacked column, effectively sparged         or distributed in packed columns, travels through the fluid and,         is vented. Gas is at 25° C., CO₂ is 2 L/min with other gases         mixed proportionally, flowing upwards through a circular 4″         diameter column; system pressures can be 1 atm psig or less.     -   (3) It can be noted by means of measuring incoming CO₂         concentration (by gas chromatograph sampling, for instance, or         with in-line measurement of CO₂ concentration) that CO₂ is being         absorbed by the fluid, that temperatures are rising (exothermic         reaction), and liquid assay sampling will show the presence of a         carbonate/bicarbonate/hydroxide equilibria, indicating that not         only absorption of CO₂ is occurring, but its conversion into         carbonate or bicarbonate form is proceeding. Practical operating         experience indicates that these key “transition points” exist in         the pH equilibria:         -   a. At pH<=8.3, the formation of bicarbonate is favored.         -   b. At pH>=10, the formation of carbonate is favored.     -   (4) The absorption/conversion to carbonate reaction proceeds         strongly and exothermically until, given the flow dynamics of         the gas, at whatever rate the CO₂ was being absorbed/converted,         the exothermic phase of the reaction ends, temperature plateaus         first and then falls, and the absorption capability of the         fluid, that falls as the OH ion concentration decreases,         effectively zeroes at this point. pH generally closely         approximates 8.3 or in its near-neighborhood when absorption         levels begin to fall; at pH>8.3, absorption is relatively         robust.     -   (5) The fluid is transferred to Bicarbonation Column 803, and         flue-gas is again introduced to the fluid. Absorption of CO₂ has         ceased and in some cases, will be shown to be negative (the         fluid gives up some CO₂ to the gas flow traveling through it).         The temperature of the fluid continues to fall, partially due to         some incidental evaporation to the migrating gas stream, but         also due to the reaction of bicarbonation that is taking place         between the previously created sodium carbonate and the         remaining “orphan” CO₂ that is dissolved in the fluid.     -   (6) The equilibrium continues to be shifted toward bicarbonate,         and optimizations of starting hydroxide concentration, fluid and         gas temperatures, pressures, flow-rates and velocities,         tortuosities, etc. can be accomplished, even up to the point of         producing pure bicarbonate (99%+).

FIGS. 2B and 2C depict the results of several test-series conducted with a charged-load (a specific concentration of NaOH was placed in a decarbonation system as shown in FIG. 2A). Several key points are demonstrated by the data in FIGS. 2B and 2C:

-   -   (1) Conditions can be modified sufficient to reproducibly create         either pure carbonate (runs 4 and 14), or pure bicarbonate (runs         28 and 32), and may be modulated to achieve various results (or         “ion ratios” between the extremes of 1.0-2.0).     -   (2) The reactor dimensions that result from this study are, for         all cases with significant absorption, found to be that         gas-liquid contact distances generally less than 3 m are         sufficient to achieve 90% absorption of incoming gases. Hence,         short, low-resistance stages are shown to be designable so as to         achieve high rates of absorption consistent with the         thermodynamic efficiency limits In other words, the physical         process of removing the CO₂ operates at absorption levels that         may apparently meet or exceed the thermodynamic efficiency of         the system. Such high absorption rates (gas in, gas out) do not         account for the energy and, therefore, CO₂-production.         Therefore, keeping CO₂ absorption rates (from the fluid) and         thermodynamic efficiency of the plant as two clearly different         measures is important to avoid confusion.

Please replace the paragraph beginning at page 36, line 28 with the following:

The results from FIGS. 2B and 2C (absorption of CO₂ by the fluid) and the product ion ratio (1.0=bicarbonate, 2.0=carbonate) are depicted in FIGS. 2D and 2E. Several important conclusions can be derived from FIGS. 2B and 2C:

-   -   (1) Instantaneous absorption-rates as high as 98% in a single         absorption-stage of incoming CO₂ are noted.         -   a. Pure bicarbonate (NaHCO₃) was produced in solution at             conditions that absorbed 25% of incoming CO₂ in a             single-stage bubble-column gas-liquid contactor with a depth             of 0.30 m fluid depth/gas-liquid contact distance.             Extrapolating to a 90% absorption, 3 meters of contact             distance is sufficient to absorb 90% of incoming CO₂.         -   b. Pure carbonate (Na₂CO₃) was produced in solution at             conditions that absorbed 70% of incoming CO₂ in a             single-stage bubble-column gas-liquid contactor with a depth             of 0.30 m fluid depth/gas-liquid contact distance.             Extrapolating to a 90% absorption, <2 meters of contact             distance is sufficient to absorb 90% of incoming CO₂.         -   c. Various absorption vs. carbonate ion ratios in products             indicate that a continuum of solutions exist between these             extremes.     -   (2) The absorbent fluid retains its absorption characteristics         for industrially-worthy lengths of time (e.g., 15-240 minutes in         these examples).     -   (3) The reactor input variables (concentration, temperature,         pressure, gas flow-rate, contact time, etc.) can be modulated to         produce pure bicarbonate, pure carbonate, or any mixture         in-between.     -   (4) Using these laboratory results to design a 90% CO₂ reactor         results in solutions under 3 m of gas-liquid contact distance         (e.g., approximately fluid depth, column height), and 1 m in         many industrial-worthy process corners.

Example 4 Analysis of LVE for Various Chemical Conditions

FIG. 5 is a chart showing low-voltage electrolysis operating lines for various chemical conditions. It depicts some typical experimental results, in which a membrane chlor-alkali cell is operated under non-standard conditions, namely:

-   -   (1) pH of the anolyte fluid (protonated brine) is adjusted by         closed-loop pH controlled addition of HCl (hydrochloric acid in         water) at pH of 1.0, 2.5, and 5.0;     -   (2) temperature of the anolyte fluid is held at setpoint, by         closed-loop fluid circuits heated by electric heaters; and     -   (3) voltage is modulated for each fluid/protonation/temperature         condition, with the current attained by the 0.01 m² chlor-alkali         cell recorded.

In FIG. 5, note the set of example experimental data, which plots actual experimental voltage vs. current (translatable into current densities, kA/m², as indicated on the chart) for a 0.01 m² electrolysis cell, 13 mm gap, operating at various combinations of temperature and degree of protonation of the anolyte brine fluid (controlled in this experimental series by closed loop ph-control of HCl(l) addition to the brine loop).

Note the following concerning these typical results in FIG. 5:

-   -   (1) At high-voltages (5V) such as are normally used in the         chlor-alkali use of such cells, the maximum current (and for a         given cell, therefore the maximum current density) is attained.     -   (2) Higher temperature brine at the same pH has a superior         current density at a given voltage.     -   (3) Lower pH brine has a superior current density at a given         voltage compared to higher pH brine.     -   (4) These general tendencies (higher temperature, higher acid         concentration) can be optimized by standard         design-of-experiments techniques for each individual         electrochemical cell geometric/component design to produce the         optimum (kA/m²V) for that cell. Similar experimentation on any         chlor-alkali cell with increased operating pressure will result         in concluding that increased operating pressure also enhances         (kA/m²V).     -   (5) The slope of the lines (ΔV/ΔA) is initially large, with         relatively large drops of voltage occurring with relatively low         drops in current/current-density; however, after an inflection         point is reached (at approximately (2.5V, 10 A/0.01 m²)),         further reductions in voltage result in more extreme reductions         in current and therefore in current density.     -   (6) This inflection-point and its near-neighborhood of operating         conditions represent the optimum voltage-vs-current-density         trade-off in an economic sense of efficiency. Standard         design-of-experiments optimization can achieve the optimum         low-voltage condition for any physical cell embodiment of the         invention.     -   (7) In the context of this example alone, that the 1.0 pH,         90° C. anolyte condition has a superior current/voltage         characteristic and is therefore the optimum operating line         represented among these various demonstrated operating lines.     -   (8) The primary drawback of low-voltage electrolysis is the         accompanying decrease in current-density; kA/m² declines with         declining voltage. Since the system must produce the same number         of Na+ ions to absorb the same amount of carbon dioxide, the m²         area of the membrane surfaces must proportionally increase;         e.g., if current density drops by 50%, then twice as much         membrane area will be required to produce sufficient absorbent         fluid. This has a serious effect on plant cost, as a         chlor-alkali plant has costs that are nearly proportional to         membrane area. Low-voltage electrolysis offers several         advantages that may, in certain embodiments of the invention,         allow optimization along low-voltage lines that redress         significantly or wholly for this large-area requirement         drawback. Namely, lifetimes of membranes and electrolytic cell         components that are operated in more benign/less energetic         operating conditions that can extend cell and/or membrane life         may be experienced. Designing specifically for lower-voltage         conditions may attend some ability to relax certain materials         and performance criteria that are not as essential in         embodiments that employ low-voltage. Certain of these         degrees-of-design freedom may result in low-cost cells that         partially or wholly absorb the incremental cell membrane cost         originally incurred due to low-voltage/low-current-density         operation. In these and many other ways, LVE systems, while         requiring larger membrane areas than standard chlor-alkali cells         for the production of the same amount of NaOH, may wholly or         partially assuage some of that additional cost and operational         expense.     -   (9) The trade-off between the benefit (lower voltage and hence         lower power) and the detriment (higher area and degrading         current density) may be optimized by the technique described in         Example 7. For the 1.0/90° C. operating line depicted in FIG. 5         (which for this small example set is the superior V/I         characteristic for LVE operation), there can be calculated a         Voptive, and from the above relationship, the IoptIve can be         obtained. Hence, for a given electrolysis cell geometric design,         conditions of temperature, pressure, brine concentration, degree         of protonation, membrane choice, etc. may all be done to produce         a superior V/I curve or operating line, and then the optimum         point on that curve can be calculated by the method of         Example 7. In this case, the VoptIve is 2.88V and the current         density IoptIve is 1.04 kA/m².     -   (10) In Example 7, the current at Vopt=2.88V is approximately 5         A in the lightly-protonated and/or low-temperature cases. In         just this example, that current (and therefore current density)         was more than doubled to 10.4 A.     -   (11) Additional protonation of the brine, temperature, pressure,         concentration, geometric arrangement of the components of the         cell, electrical fields, and conditions can be similarly         optimized to produce a superior (kA/m²V) metric, but protonation         itself increases the amount of stoichiometric hydrogen produced,         thereby increasing the energy pay-back of the system. It is         important to note that optimizing for the lowest-energy CO₂         absorption/conversion can be attained by both optimizing the         (kA/m²V) of the system, which lowers the energy required to         manufacture the absorbent fluid, but that simultaneously         optimizing the hydrogen available for energy-recovery (and then         optimizing the efficiency by which that available hydrogen         energy is recovered), the entire energy for the process may be         optimized to its lowest potential, for a given physical         electrochemical cell of specific design.     -   (12) Given that embodiments of the present invention can         effectively absorb CO₂ in extremely dilute hydroxides (0.2 M and         less have been demonstrated) compared to the concentrated         hydroxide normally produced in chlor-alkali manufacture         (typically 33-35% by weight, then concentrated further by         steam-evaporation), the design of chlor-alkali cells for         low-concentration operation (as well as low-voltage operation)         may provide new degrees of freedom for design optimization at         these non-standard conditions.

Embodiments of the present invention are incapable of making more hydrogen-energy than the energy consumed in making that hydrogen. Otherwise, a violation of the Second Law of Thermodynamics would result. This places a limit on the minimum voltage that can be applied to the electrochemical cell. Presuming 100% efficiency on the hydrogen return, and using 39000 kw-hr/ton H₂ energy content (EIA reference value), would result in a minimum voltage of 1.55V. A person of skill in the art can, for any system with a given hydrogen/electric return efficiency and a chosen value for the energy content of the system, compute a minimum achievable voltage for that system.

In practice, thermodynamic inefficiencies (including but not limited to, I2R losses, current inefficiency in the cell, waste-heat losses, etc.), and the requirement of slight over-voltage to operate, raise the minimum voltage attainable for a given cell. The above figures vary slightly depending upon the value of “a,” the protonation ratio, as it varies the amount of hydrogen available for energy-recovery.

That said, current-density at low-voltage determines the amount of electrolysis area (a good scalar for capital expense) required to produce an amount of caustic, and at minimum voltage, the area required is extremely large. Hence, some voltage above minimum voltage is required for operation, the amount depending upon the capital-expense/ecological-efficiency trade-off chosen in the design. Current efficiency (the percent of current spent in manufacturing product) declines at low voltage, so optimizing low-voltage electrolysis operation is not the same as attaining a single low-voltage operating condition. Current processes are designed to operate in the LVE regime (below 5V), and at these voltages below 5V power consumption over traditional techniques is significantly enhanced.

Example 5 Thermodynamics of a Large-Scale Plant Design

For this example, a model plant (incorporating certain embodiments of the present invention) exhibiting full-scale operating plant behavior is explained and the energy required to extract a given amount of CO₂ quantified and bounded within statistical limits by various means and methods, including the following:

-   -   (1) Thermodynamic efficiency (∂CO₂/∂E) can be approximated as         ΔCO₂/ΔE over sufficiently short range intervals of E (energy).     -   (2) Certain simplifying assumptions can be made regarding a         plant design such as is represented in FIG. 9A, among them:         -   a. The primary energy spent is in the electrolysis process;             pumping, compression, controls, etc. are considered de             minimis relative to the energies spent making reactants             (electrolysis) and in hydrogen energy-recovery. These values             assumed zero or <0.1% of power consumed in electrolysis             operations.         -   b. Electrolysis energies spent can be represented             approximately by the following equation:             Eout=V*I*EFFcurrent         -   Where:             -   V=voltage of operating electrolysis cell             -   I=current required to produce the chemicals by                 electrochemical half-reaction, including the                 greater-than-1:1 stoichiometry caused by the protonation                 of the brine. 0.05HCl/NaCl ratio of protonating ions                 consumed in electrolysis is used in the example.             -   EFFcurrent=the current efficiency, defining the amount                 of current used in the actual production of chemical                 species, with the remainder being lost in I2R losses,                 etc. 97% is the value used in the example; each                 electrolysis cell will have its own unique current                 efficiency, which degrades and varies over the life of                 the cell.         -   c. Energy recovered from hydrogen-combustion (by whatever             means, combustion as a boiler gas, combustion in a             fuel-cell, etc.) as:             Ein=39000 kw−hr/toncompressed H2*Ton H2*EFFdc         -   Where:             -   Ton H2=tons of hydrogen produced by the process                 including the hydrogen produced by the greater-than-1:1                 stoichiometry, caused by the protonation of the brine.             -   EFFdc=the efficiency of the hydrogen-recovery process in                 converting the incipient energy of the hydrogen gas into                 DC electric current. 60% of the hydrogen-energy produced                 is recovered into DC current. This is the current                 off-the-shelf DC efficiency of hydrogen/atmospheric                 oxygen fuel cells; a similar number is obtained for the                 process of compressing the hydrogen (which costs 15% of                 its power to accomplish) and then assuming 85% of the                 hydrogen energy is returned in the customer processes                 such as hydrogenation processes, gasoline reforming                 processes, etc.         -   d. Energy returned from waste-heat recovery salvaged from             the heat of the incoming flue-gas stream. Incoming heated             gases are cooled once entering the process. In some             embodiments of the invention, this cooling can be             accomplished by absorption of the waste-heat and the             conversion of that heat into electrical DC energy, which can             be used to supplement/fully-power/over-power the process             that composes the invention. In this example, the             supplemental waste-heat recovery is not included.

The plant model for this example includes a modeling of the flue-gas exiting the power-plant under normal operating conditions, as shown in FIG. 9B. This involves significant assumptions regarding the composition of the fuels, the efficiency of the combustion processes themselves, the relative proportion of elements in the combustion processes, etc. The assumptions for this example are depicted in FIG. 9B and are consistent with the flue-gas output of a typical sub-bituminous coal-fed power-plant with a 10,000 BTU/kw-hr heat-rate.

For a given flue-gas output, there is a hydroxide requirement that can be calculated. Several assumptions are required here. The ratio of ions (“ion ratio” is the ratio Na/C in the absorption/conversion reaction) is the same as the ratio of those elements in the product solids formed. In the case of pure bicarbonate, the number would be 1.0, in the case of pure carbonate, the number would be 2.0, and for mixtures of bicarbonate and carbonate, the number would lie between 1.0 and 2.0. The calculation for the caustic requirement for this example is depicted in FIG. 9C. For the example depicted in FIG. 9C, the ion ratio is 1.0.

For a given hydroxide requirement, there is a corresponding electrolysis requirement, based upon the amount of water, salt, square meters of membrane surface (the scalar for electrochemical cells of this kind), and current density (itself a function of the cell design, chemistry, and operating conditions; here the figure of 3 kA/m² is used). These calculation of the electrolysis requirement for this example is depicted in FIG. 9D.

For a given amount of electrolysis under protonated conditions, there is a given amount of hydrogen gas produced, which itself represents a certain amount of energy available for recovery, or the hydrogen is used chemically in further processing. In this example, the hydrogen is converted to DC electricity using a fuel cell operating at EFFdc=60%.

For a given amount of flue-gas processed, there is a certain waste-heat content that can be extracted from it at a certain efficiency of conversion into DC electricity, and that recovered electricity may be used to supplement the DC electricity consumed by the process in electrolysis. The waste-heat for this example is depicted in FIG. 9E, with an efficiency chosen, in this case, of 25%, a figure that is exceeded by various waste-heat/DC generation techniques extant in the field.

Given these individual components of energy inputs and outputs, the net effect of these energy transfers may be summed, as in FIG. 9F. Here, energies are presented in kw-hrs and as percentages of the basis-plant power, and a calculation of ecological efficiency for this example is shown.

In some embodiments of the present invention, an additional H₂/Cl₂ fuel cell may be employed to combust hydrogen and chlorine gases for the purpose of recycling HCl used for protonation of the brine. In particular, the amount of “super-stoichiometric” HCl can be recycled, and in theory, eliminate the need for stock chemical HCl to be added to the system. In actual practice, a certain amount of make-up HCl must be periodically added to the system. The combustion of H₂ in Cl₂ contains more energy than does the H₂/O₂ combustion. Slight additional energy is thereby attained. However, fuel-cells are inherently somewhat less-than-perfectly efficient, so the energy “gain” from using chlorine as the oxidant is more than outweighed by the loss inherent in the recovery method. Hence, in this example, these effects are considered to cancel each other out, and are zeroed. Therefore, the two effects somewhat offset each other but still result in a net loss. However, the effect of the presence of the additional protons in the electrolysis is to dramatically catalyze the production of NaOH at low voltages and high (kA/m²V) at those low voltages. Hence, for any given apparatus, an optimization can be carried out to recycle a given amount of H₂/Cl₂ into HCl and to protonate the incoming brine with that amount of HCl. At some optimum value (usually found between a=0.05 and a=1.0M, or near pH=1 at 90° C.), hydrogen/chlorine fuel cell losses (which outweigh the slight gain over oxygen oxidation presented by the chlorine) and hydroxide energy benefits (better kA/m²V) will be simultaneously optimum for the entire system. It should be noted that in this example, only H₂/O₂ combustion is calculated; the H₂/Cl₂ combustion has a slight thermodynamic gain from the extra strength of the chlorine oxidation, but the countering effect of fuel-cell inefficiency makes for a slightly negative, but considered de minimis, effect.

A. Calculation of Ecological Efficiency

Calculation of ecological efficiency (∂CO₂/∂E) and ΔCO₂/ΔE for this example was accomplished as follows:

-   -   (1) It was presumed that there were three plants:         -   a. The basis power plant (exemplified in the flue-gas model             in FIG. 9B)         -   b. The CO₂ Absorption/Conversion plant (which requires             supplementary power to process the flue-gas from the basis             power plant and returns a portion of that power from             hydrogen combustion or the calculated power inherent in             hydrogen, if hydrogen is the end-product and is not             combusted).         -   c. A third, supplemental power-plant that provides the power             required by the CO₂ Absorption/Conversion plant. In this             example, the characteristics of this power plant were             assumed to be identical to the basis plant.     -   (2) The following aspects relating to the CO₂ and energy spent         in processing 100% of the basis plant were then calculated:         -   a. CO₂ from the basis plant (flue-gas model)         -   b. Energy produced by the basis plant         -   c. Net energy required by the CO₂ absorption/conversion             process         -   d. Net energy required by the supplemental power plant is             assumed identical to the Net energy required by the CO₂             absorption/conversion process.         -   e. CO₂ produced by the supplemental plant is assumed to be             proportional to the energy produced by the supplemental             plant, and with the same ΔCO₂/ΔE of the basis plant.     -   (3) The following results for the above calculations were         obtained:         -   a. Basis Plant—a 10,000 heat-rate plant producing 1 Gw             continuously for a 1-year basis produces 8.76 Bkw-hrs each             year and produces a basis of 7,446,068 tons of CO₂ per year,             averaging 1176 kw-hr/ton CO₂.         -   b. CO₂ Absorption/Conversion Plant—for this example             calculation (a=0.10, 2.1V operation, pure bicarbonate             produced, 15% of hydrogen energy consumed in compression,             pumping/compression costs and waste-heat recovery benefits             excluded), 3.648 BKw-hr are required to absorb/convert 100%             of the basis plant.         -   c. Supplemental Power Plant—the plant in this example             produces the power required by the CO₂ Absorption/Conversion             Plant, 3.648 Bkw-hr, and itself produces (by the 1176             Kw-hr/ton CO₂ figure from above) a total of 3,101,209 tons             of CO₂ that is presumed to be emitted to the atmosphere.         -   d. Total power generated is therefore 12.48 Gw-hrs. Total             delivered power is therefore 8.76 Gw-hrs. Total CO₂             generated is therefore 10.55 Mtons. Total CO₂ emitted is             therefore 3.101 Mtons. 29.1% of total power is consumed in             the CO₂ absorption/conversion process. 71.9% of total CO₂ is             consumed.

Several key points are illustrated by the above calculations:

(1) Arithmetically, it is demonstrated that the following formulae apply: % power consumed=1−% CO₂ consumed % CO₂ consumed=1−% power consumed

-   -   This forms a line, called the One Unit Operating line, shown in         FIG. 9A.

(2) For this example, the (∂CO₂/∂E) and ΔCO₂/ΔE are algebraically identical, namely: ΔCO₂/ΔE=(∂CO₂/∂E)=0.291/0.719=0.41

Further extrapolated cases can be further modeled, in which cases, the CO₂ emitted by the Supplemental Power Plant is itself treated by another CO₂ absorption/conversion process unit #2 of correspondingly smaller capacity, and that absorption/conversion unit #2 is correspondingly powered by a Supplemental Power Plant #2, etc., which results in results like those in Table 2 for the first five series of iterations.

TABLE 2 Power Produces Produces Amount Inc Power Plant CO₂ (Mton) Power (kw-hr) Absorbed Required Basis 7,446,068 8,760,000,000 7,446,068 3,648,448,267 Iteration 2 3101209 1519540497 Iteration 3 1291621 632872705 Iteration 4 537947 263584854 Ecological Power Supplemental Efficiency Plant CO₂ % tot E % tot CO₂ (∂CO₂/∂E) Basis 3101209 29% 71% 2.40 Iteration 2 1291621 37% 89% 2.40 Iteration 3 537947 40% 96% 2.40 Iteration 4 224049 41% 98% 2.40

Several points regarding Table 2 are significant to the model:

-   -   (1) Note that the efficiency of the process, whether in the         basis case, or any of the successive iterated cases,         consistently produces the same (∂CO₂/∂E) value for the system;         this term is considered constant for systems that approximate         the constraints of this model and is called, for these purposes,         the ecological efficiency of the process.     -   (2) It is clear that the value (∂CO₂/∂E) is constant in all         solutions, so a solution can be derived when then number of         iterations is presumed infinite; i.e., when the plant is         operated so as to consume 100% of the CO₂ produced by the plant,         by the simple expedient of using the following equation:         1/(∂CO₂/∂E)=% of plant power required to absorb/capture 100% of         produced CO₂         -   In the example case, this calculates as 41.6%.     -   (3) Alternatively, it is evident that, when the net power spent         in absorption/conversion is zero (neglecting waste-heat         recovery), for a given process condition, the CO₂ absorbed and         converted is likewise zero. Hence, all operating lines for         plants of this type theoretically intersect at (0% Power, 0%         CO₂).     -   (4) Given any two points in a linear system, straight-line         solutions for Operating Lines may be constructed that define the         operating characteristics of the CO₂ Absorption/Conversion         process, by the following means:         -   a. for each operating condition, a basis-case solution is             accomplished, and the resulting point One Unit Case solution             (% Power, % CO₂) is plotted on a graph of % CO₂ (y-axis) vs.             % Net Power consumed x-axis);         -   b. for that case, (∂CO₂/∂E) is calculated, and the case at             y=100% is solved for the x-coordinate; and         -   c. all lines are presumed to travel through the origin. In             actual systems, there would be some power consumption             (controls, environment, etc.) at even zero absorption, so             this is an idealized case. In practice, these lines would be             slightly curved and not terminate at the origin.     -   (5) In this way, a family of operating lines for CO₂         absorption/conversion processes of this type can be created.     -   (6) On this same type of plot, competing technologies can also         be plotted and compared graphically, e.g.:         -   a. A competing MEA (methyl-ethyl-amine) absorption             technology consumes 30% of plant power to accomplish an             absorption of 58% of CO₂ emitted before absorption was             introduced.         -   b. Further, an estimated 15% of plant power is expended in             liquefying this CO₂ through extreme pressure and             refrigeration cycling (45% power/58% CO₂).         -   c. This would then demonstrate a (∂CO₂/∂E) value of 1.24;             however, there is additional unaccounted energy required to             transport/inject/maintain the CO₂ in a sequestration-site.         -   d. Graphically, this competing technology is shown to be             less efficient than the example CO₂ absorption/conversion             plant operating the process which is one embodiment of the             invention; i.e., this model shows the competing technology             would require 70%+ of the power plant to eliminate 100% of             its CO₂ production. Note these points regarding the             competing technology as graphically represented in FIG. 9A             (refer to legend on chart):             -   i. According to 2005 EIA estimates, the absorption of                 CO₂ by a MEA technology requires 30% of the plant power                 to absorb 58% of the flue-gas CO₂ produced. (Note                 position on chart in FIG. 9A (30%, 58%) for                 absorption-processing alone.)             -   ii. By the same estimates, compression/liquification of                 that CO₂ consumes another 15% of the plant power, moving                 the operating point of such a plant to (45%, 58%).             -   iii. There is no firm estimate of the energy required to                 transport the liquid CO₂ by pipeline or other                 transportation device, nor for that matter the amount of                 energy necessary to pump or inject that CO₂ into a                 carbon store of various natures, nor the amount of                 energy that might be required to maintain that CO₂ in                 said stores for perpetuity. However, though those                 additional energies are not estimable, it seems                 reasonable to assume they are non-zero. Hence, the                 ecological efficiency of such a device is logically                 worse than a (45%/58%) trade-off in power-spent to                 secure a certain CO₂-reduction benefit. Extrapolating                 this to a 100% remission case, the                 MEA/liquification/sequestration technique would consume                 more than 70% of the plant power. It should be noted                 that typical competing absorption technologies cannot                 approach 100% absorption; i.e., the figure of 58% CO₂                 absorption was for a plant that processed 100% of                 outgoing flue-gas.

B. Calculation of the Limits of Ecological Efficiency [(∂CO₂/∂E)max]

In practice, for a given system that effectively converts all the NaOH produced to NaHCO₃ by absorbing CO₂, the primary energy component is the kw-hr/moleNaOH. Although the power per mole NaOH is proportional to both voltage and current, the current is fixed by the stoichiometry of the chemistry. Thus, the power expended per mole CO₂ is primarily optimized by achieving the lowest voltage condition that efficiently produces hydroxide.

The minimum voltage at which an electrolysis system according to embodiments of the present invention operates (as configured with varying concentrations, geometric dimensions, flow-rates, etc.) can be determined by observing the Current-Density (kA/m²) vs. V characteristics of the system and determining the lowest voltage at which sufficient, non-zero current densities are obtained to make product. Altering the physical dimensions, electrical field generation devices, cell geometries, compositions of materials, and processing conditions to optimize this characteristic metric (kA²/m²V) is a primary means to optimize these systems, and typical design-of-experiments techniques are useful for optimizing an industrial process for a given physical plant.

Practical limitations aside, there is one fundamental limit that will apply to all systems with a given H/Na ratio (protonation ratio), namely:

-   -   (1) No device can operate that produces more energy through         hydrogen-energy recovery than is input to the system in         electrolysis. Persons familiar with thermodynamic principles         will note this would be a “Second Law Violation.”     -   (2) As a result of this fact, a fundamental thermodynamic limit         can be bounded, given a choice of H/Na ratio used in the anolyte         consumption:         -   a. For this example, H/Na was presumed to be 0.10.         -   b. The hydrogen energy return efficiency was set at 100%.         -   c. The lowest voltage at which operation can occur, in which             the net energy consumed by the system is zero (“Vmintheo”)             (i.e., the point where electrolysis costs equal the assumed             100% hydrogen return efficiency), was calculated.         -   d. In this example, that low voltage is 1.5526V. This number             is a strong function of the Na/C ratio, the H/C ratio, and             the hydrogen-energy return efficiency. In this optimal case,             Na/C is 1.0 and H/C is 1.0.         -   e. Following this calculation through to its ecological             efficiency, the Single Unit solution is approximately 7%             power for 93% CO₂ absorption/conversion.         -   f. Processing at more efficient operating points than this             theoretical minimum is possible by:             -   i. supplementing the power consumption with waste-heat                 recovery; and             -   ii. powering the absorption/conversion process either                 partially or wholly with power whose production does not                 cause CO₂ emission (hydro-electric, solar, wind,                 nuclear, etc.).

Similarly, presuming ideal hydrogen-return efficiency, etc. as above, the maximum voltage at which operation can be “ecological” (“Vmaxeco”) (i.e., in which the CO₂ absorption/conversion process removes more CO₂ than it creates) was calculated:

-   -   a. H/Na, Na/C, and hydrogen return energy efficiency were set at         1.0, 1.0, and 100%, respectively, as above.     -   b. The voltage at which the CO₂ removal would be 50% was         calculated.     -   c. In this example, that Vmaxeco is 4.457V. At this voltage and         condition, the process operates on the line ∂CO₂=∂E, the         boundary between ecologically beneficial and ecologically         harmful operation.

Hence, ecologically-beneficial operation will occur when the electrolysis system is operated between Vmintheo (1.5526V) and Vmaxeco (4.457V). Operation between those two points may be replicated with many typical electrolysis systems. Laboratory results at or below 2.1V may be readily reproduced by manipulation of geometry, concentration, temperature, pressure, flow-rate, etc. of electrochemical cells designed in this fashion.

C. The Effect of Non-Greenhouse-Generating Power on Ecological Efficiency

Where the supplemental power (that which powers the process) is produced by non-greenhouse-gas (GHG) emitting power (e.g., wind-power, hydro-electric, solar, nuclear, etc.), then there are zero supplemental CO₂ emissions, and the ecological efficiency of the present invention is vastly improved. For this example, the term 3101209 tons of CO₂ in Table 2 is eliminated along with all the subsequent iterations, etc., leaving this simplified result: all CO₂ is absorbed/converted (7,446,069 tons), and the total power required is simply the 8,760,000,000 basis plus the 3,648,448,267 kw-hrs required to accomplish the work necessary to absorb/convert that basis amount of CO₂, requiring only 29% of total power to secure 100% of the CO₂ emissions in the non-GHG-powered process, compared to 41% of total power to secure 100% of the CO₂ emissions in the GHG-powered process. This means that embodiments of the present invention provide a significant “leverage” factor when the process is powered by non-GHG emissions. Rather than using non-GHG power to displace GHG-generating power on a 1%:1% basis, if the non-GHG power is instead used to power processes that are some embodiments of the present invention, 1% of non-GHG-generating power then displaces GHG-generation by a multiplied factor, even in excess of the GHG-generating power examples described herein. One can easily envision cases in which, for a given nation, state, or entity, a certain proportion of non-GHG-generating power, when used in this magnified fashion, could more efficiently attain any CO₂ reduction goal; i.e., one could use “clean” power in a highly leveraged manner to clean-up the emissions of other “dirty power.”

Given that in some applications, non-GHG-producing power generation is available, sometimes in sporadic forms (e.g., solar, wind-power “farms”, etc.), the ability to utilize that power to make large quantities of absorbent during off-peak periods is extremely advantageous.

Example 6 Ecological Efficiency of Various Modeled Power Plants

FIG. 10 shows the ecological efficiency of various modeled power plants incorporating embodiments of the present invention, and it depicts various conditions that are the primary factors in determining the ecological efficiency, (∂CO₂/∂E).

From these calculations it can be generally concluded that:

-   -   (1) Forming sodium carbonate and using standard chlor-alkali         conditions, the process would have an ecological efficiency >1,         and while such an operation might be economically viable, it         produces more CO₂ than it absorbs.     -   (2) Altering the product equilibrium to favor the production of         sodium bicarbonate improves the ecological efficiency of the         process. In the case of altering conditions so as to produce         virtually pure sodium bicarbonate this advantage is         fully-optimized     -   (3) Adopting low-voltage electrolysis practice firmly moves the         process into an operating region characterized by ecological         efficiencies lower than 1.0 (i.e., ecologically beneficial CO₂         absorption and conversion processes). Optimizing each physical         emulation of the electrolysis system for optimum (kA/m²V) and         maximum hydrogen energy production leads to further improvement         in ecological efficiency.     -   (4) Coupling the absorption/conversion process of embodiments of         the present invention with any number of available or         created-for-purpose machines that convert waste-thermal heat to         DC electricity, the initial energy investment in DC electrolysis         and AC pumping, etc. may be supplemented or wholly supplied from         the waste-heat recovery.

It should be noted that supplying the invention with power from non-green-house gas emitting power generators allows the process to directly approach 100% CO₂ absorption (see discussion in Example 5).

Example 7 Determining VoptIve (the Optimum Low-Voltage Operating Voltage with Respect to Cell-Capacity or Area) and IoptIve (the Current at that Operating Voltage), Given a V/I Characteristic Operating Line for an Optimized LVE Chlor-Alkali Cell

It has been demonstrated herein that lower-voltage operation lowers the power required to manufacture sodium hydroxide that is used as an absorbent fluid. Table 3 shows calculations made from the V1 operating line of the 1.0/90° C. anolyte case in FIG. 5 (discussed above in Example 4.).

Several points should be noted regarding the contents of Table 3:

-   -   (1) The third column, current efficiency (dimensionless),         represents the proportion of current generated that is used in         producing product chemicals; losses, such as I2R losses and         waste heating of electrolytic fluids are the primary cause of         inefficiencies. Current efficiency declines with declining         voltage.     -   (2) Cell area is normalized for a 3.975V case (where the current         density, and therefore the area requirement of the process, is         identical to a std 5V electrolysis running with 3.0 kA/m²         characteristic). A2/A1 (dimensionless) is calculated.

The last term, % of power-saved per dimensionless area, is plotted in FIG. 11. For such a function, the point at which the maximum slope (change in power usage per change in voltage) represents an optimum; i.e., at low voltage (e.g. 2.1-2.5V) the slope (Δpower/Δm²) is relatively low, then at higher voltages (e.g. 2.5 to approximately 3), the slope (Δpower/Δm²) increases to a larger value, and then declines to lower slopes as the voltage continues to increase. This illustrates that there is a region of high-slope bounded by a region of low-slope on each side; i.e., on either side of that VoptIve point, the change in power usage per voltage delta is less effective.

A function that closely approximates the actual behavior was accomplished first (note the formula of the polynomial trend-line produced by least-squares fit). In this example: y=−10.164x3+88.256x2-235.06x+198.37 is a close-approximation. Then, the first-derivative of the function was calculated by typical treatment of polynomials: dy/dx=(3)(−10.164)x2+(2)(88.256)x−235.06=max. Values of x (Volts) can be iterated to find the maximum of this first derivative, which can be accomplished by various techniques, resulting in 2.894V as the solution.

Note that voltages lower than 2.894V may be employed, and further power savings will result. Some preferred embodiments will optimize low-power operation below this “natural optimum point.” In those cases, the additional area used in the membrane will result in a “sub-optimized” electrolysis system, but low-power operation for the overall decarbonation process may be further benefited by operating below this natural optimum for a given electrolysis sub-system. However, when doing so, the voltage/power benefit is thereafter attenuated, while the area-factor continues to proportionally make operation less efficient per area.

The current and current density that corresponds to this VoptIve can be determined by either forming a similar least-squares relationship for V and I, or by graphically using the operating curve to determine IoptIve. In this example, the calculated value is 10.419 A (or for a 0.01 m² cell area, as in this case), 1.042 kA/m².

TABLE 3 Volts, V operating I, conditions: Power = Current Anolyte pH 1.0, Current Δ(kA/m²)/ ΔPower/ V * I * (A) 90 Deg. C. Efficiency ΔV Δ(kA/m²) Eff 30 3.975 97% 1.82 0.55 115.67 25 3.7 96% 1.87 0.53 88.83 20 3.433 94% 1.87 0.54 64.62 15 3.165 91% 1.80 0.56 43.34 10 2.887 88% 1.79 0.56 25.30 7.5 2.747 83% 1.74 0.58 17.15 5 2.603 78% 1.69 0.59 10.19 4 2.544 73% 1.49 0.67 7.41 3 2.477 67% 1.43 0.70 4.98 2 2.407 60% 1.19 0.84 2.90 1.5 2.365 54% 0.89 1.12 1.92 1 2.309 49% 0.64 1.57 1.13 0.7 2.262 44% 0.61 1.65 0.70 0.5 2.229 40% 0.62 1.60 0.44 0.4 2.213 36% 0.32 3.10 0.31 0.3 2.182 32% 0.56 1.80 0.21 0.2 2.164 29% 0.23 4.40 0.12 0.1 2.12 26% 0.00 212.00 0.05 I, % Power Current Cell Area % of STD Saved by (A) A2/A1 Power/kgmole Reduced V Δpowersaved/m² 30 1.000 77% 23% 25 1.302 71% 29% 22.22 20 1.790 65% 35% 19.77 15 2.669 58% 42% 15.82 10 4.572 51% 49% 10.80 7.5 6.744 46% 54% 8.05 5 11.357 41% 59% 5.22 4 15.619 37% 63% 4.03 3 23.248 33% 67% 2.87 2 39.873 29% 71% 1.78 1.5 60.121 26% 74% 1.24 1 102.631 23% 77% 0.75 0.7 166.292 20% 80% 0.48 0.5 262.506 18% 82% 0.31 0.4 367.228 16% 84% 0.23 0.3 551.770 14% 86% 0.16 0.2 927.267 12% 88% 0.09 0.1 2103.359 11% 89% 0.04

All of the methods and devices disclosed and claimed herein can be made and executed without undue experimentation in light of the present disclosure. While the methods and devices of this invention have been described in terms of preferred embodiments, it will be apparent to those of skill in the art that variations may be applied to the methods and devices and in the steps or in the sequence of steps of the method described herein without departing from the concept, spirit, and scope of the invention. More specifically, it will be apparent that certain compositions which are chemically related may be substituted for the compositions described herein while the same or similar results would be achieved. All such similar substitutes and modifications apparent to those skilled in the art are deemed to be within the spirit, scope, and concept of the invention as defined by the appended claims.

REFERENCES

The following references, to the extent that they provide exemplary procedural or other details supplementary to those set forth herein, are specifically incorporated herein by reference.

-   “Annual Energy Outlook 2005 (AEO2005),” prepared by the Energy     Information Administration, available through National Energy     Information Center, EI-30, Washington, D.C. -   “Carbonate Chemistry for Sequestering Fossil Carbon,” by Klaus S.     Lackner, in Annual Review of Energy Environment, 2002, by Annual     reviews. -   “Effects of the Operating Pressure On The Performance of     Electrolytic Cell at Elevated Temperatures,” by Y. Ogata, M. Yasuda,     and F. Hine, Nagoya Institute of Technology, Japan. In Proceedings     of the Symposium on Electrochemical Engineering in the Chlor-Alkali     and Chlorate Industries, The Electrochemical Society, 1988. -   “Electrochemical Hydrogen Technologies—Electrochemical Production     and Combustion of Hydrogen,” edited by Hartmut Wendt, Institute fur     Chemische Technologie, Stuttgart, Elsevier Press 1990. -   “Electrochemical Process Engineering—A Guide to the Design of     Electrolytic Plant,” by F. Goodridge and K. Scott, University of     Newcastle upon Tyne, 1995. -   “Exergy Study of the Kalina Cycle,” by Goran Wall, Chia-Chin Chuang,     and Masaru Ishida, presented at 1989 American Society of Mechanical     Engineers (ASME), Winter Annual Meeting, San Francisco, Calif.,     December 1989, published in “Analysis and Design of Energy Systems:     Analysis of Industrial Processes AES Vol. 10-3, pp 73-77 ASME. -   “Industrial Electrochemistry,” 2^(nd) Edition, edited by Derek     Pletcher and Frank Walsh, 1990. -   “Modern Chlor-Alkali Technology,” edited by M. O. Coultier, Society     for the Chemical Industry, London, 1980. -   “Modern Chlor-Alkali Technology,” Volumes 1-7, The Royal Society of     Chemistry Information Services, 1998. -   “Some Guidelines for Analysis, Design, and Operational Principles of     Bubble Column Reactors,” and other selected information contained in     “Bubble Column Reactors,” by Wolf-Dieter Deckwer, Gesellschaft fur     Biotechnologische Forschung mbH, Braunsweig, Germany, translated by     Robert Field, 1991 ISBN 0-471-91811-3. -   “Transport and Structure in Fuel Cell Proton Exchange Membranes,” by     Michael Anthony Hickner, dissertation submitted to the faculty of     Virginia Polytechnic Institute and State University, 2003. -   FIG. 8. “CO2 Absorption vs. (Low) Interfacial Gas Velocity at     Various Column Heights of 0.18 M Sodium Hydroxide Solution in an     Unpacked Sparged Bubble Column,” from A. Schumpe thesis, University     of Hanover, 1978. -   Klara in: EIA Emissions of Greenhouse Gases in the U.S. 2000, EPGA     3^(rd) Annual Power Generation Conference, Hershey Pa., 2002. -   Mandal, et al., J. Chem. Engineering (Canada), 81:212-219, 2003. -   Shah et al., AiCHE J., 28(3):353-379, 1982. -   Unit Operations of Chemical Engineering, McGraw-Hill, 3^(rd) edition     © 1976, “Gas Absorption” pp. 707-743, after Eckert. -   Wie-rong et al., J. Zhejiang University Science, ISSN 1009-3095,     2004. 

What is claimed is:
 1. A method of sequestering carbon dioxide produced by a source and contained in a gas stream, comprising the steps of: (a) obtaining a hydroxide in an aqueous mixture; (b) admixing the hydroxide with carbon dioxide produced by the source to produce bicarbonate products or a combination of carbonate and bicarbonate products in an admixture; (c) separating said products from the admixture, thereby sequestering the carbon dioxide in a mineral product form; and (d) using said products to perform ion-exchanges with one or more group-1 or group-2 salts to precipitate carbonates; wherein obtaining the hydroxide comprises: obtaining a group-1 or group-2 salt; admixing the salt with acid and water, acid and steam, or acid, water, and steam to produce a protonated brine solution; and electrolyzing the protonated brine solution to produce a hydroxide; wherein step (b) comprises altering the product equilibrium to favor the production of bicarbonate products.
 2. The method of claim 1, wherein an amount of carbon dioxide is generated in performing steps (a)-(c), and that amount of carbon dioxide is less than the amount of carbon dioxide sequestered in performing steps (a)-(c).
 3. The method of claim 1, wherein the admixing occurs in two separate chambers, with one chamber being used to produce carbonate products and the other chamber being used to produce bicarbonate products.
 4. The method of claim 1, wherein the admixing occurs in a bubble column or series of bubble columns.
 5. The method of claim 1, wherein step (c) involves a heated-precipitation separation process.
 6. The method of claim 5, wherein the heat for the separation process is derived from heat exchange with incoming flue-gases.
 7. The method of claim 1, further comprising: transporting the products to a remote sequestration site; combining the products with acid in a neutralization reaction to generate pure carbon dioxide; and injecting the carbon dioxide into a carbon bank.
 8. The method of claim 1, wherein other components of the gas stream are neutralized and/or captured in performing steps (a)-(c).
 9. The method of claim 1, wherein electrolyzing the protonated brine comprises combusting a carbon-based fuel source to produce DC electricity.
 10. The method of claim 1, wherein the amount of acid admixed with the salt is based on a determination of the optimum protonation rate that achieves the lowest energy to produce reactants and the highest energy to recover from products.
 11. The method of claim 1, wherein: the protonated brine solution is electrolyzed in an electrochemical cell having a catholyte side and an anolyte side; and the products are recycled to the catholyte side of the electrochemical cell.
 12. The method of claim 1, wherein the energy required by the method is supplemented with waste-heat recovered from the gas stream.
 13. The method of claim 1, wherein the salt is sodium chloride, the acid is hydrochloric acid, and the hydroxide produced by electrolyzing the protonated brine solution is sodium hydroxide.
 14. The method of claim 1, wherein the gas stream is an exhaust stream from a plant.
 15. The method of claim 14, wherein the plant is a power plant that employs a carbon-based fuel source.
 16. The method of claim 13, wherein electrolyzing the protonated brine solution also produces chlorine gas and hydrogen gas.
 17. The method of claim 16, wherein the chlorine gas and hydrogen gas are combusted to form hydrochloric acid.
 18. The method of claim 16, wherein the hydrogen gas is used to produce energy.
 19. The method of claim 17, wherein the hydrochloric acid formed from the chlorine gas and hydrogen gas is used in obtaining additional hydroxide.
 20. The method of claim 16, wherein the hydrogen gas is combusted with atmospheric oxygen or oxygen from stock chemicals to produce water.
 21. The method of claim 18, wherein step (c) involves a heated-precipitation separation process in which the heat for the separation process is derived from the energy produced by the hydrogen gas.
 22. The method of claim 18, wherein the hydrogen gas is co-burned with coal to improve coal-fired emissions.
 23. The method of claim 18, wherein the hydrogen gas is used in a combustion process for fuel-cell recovery of DC electricity.
 24. A method of sequestering carbon dioxide produced by a source and contained in a gas stream, comprising the steps of: (a) obtaining a hydroxide in an aqueous mixture; (b) admixing the hydroxide with carbon dioxide produced by the source to produce bicarbonate products or a combination of carbonate and bicarbonate products in an admixture; and (c) separating said products from the admixture, thereby sequestering the carbon dioxide in a mineral product form; wherein obtaining the hydroxide comprises: obtaining a group-1 or group-2 salt; admixing the salt with acid and water, acid and steam, or acid, water, and steam to produce a protonated brine solution; and electrolyzing the protonated brine solution to produce a hydroxide using diaphragm, mercury, or membrane cells; wherein step (b) comprises altering the product equilibrium to favor the production of bicarbonate products.
 25. A method of sequestering carbon dioxide produced by a source and contained in a gas stream, comprising the steps of: (a) obtaining a hydroxide in an aqueous mixture; (b) admixing the hydroxide with carbon dioxide produced by the source to produce bicarbonate products or a combination of carbonate and bicarbonate products in an admixture; and (c) separating said products from the admixture, thereby sequestering the carbon dioxide in a mineral product form; wherein obtaining the hydroxide comprises: obtaining a group-1 or group-2 salt; admixing the salt with acid and water, acid and steam, or acid, water, and steam to produce a protonated brine solution; and electrolyzing the protonated brine solution to produce a hydroxide and hydrogen gas; wherein step (b) comprises altering the product equilibrium to favor the production of bicarbonate products; wherein the hydrogen gas is traded or sold.
 26. A method of sequestering carbon dioxide produced by a source and contained in a gas stream, comprising the steps of: (a) obtaining a hydroxide in an aqueous mixture; (b) admixing the hydroxide with carbon dioxide produced by the source to produce bicarbonate products or a combination of carbonate and bicarbonate products in an admixture; and (c) separating said products from the admixture, thereby sequestering the carbon dioxide in a mineral product form; wherein obtaining the hydroxide comprises: obtaining a group-1 or group-2 salt; admixing the salt with acid and water, acid and steam, or acid, water, and steam to produce a protonated brine solution; and electrolyzing the protonated brine solution to produce a hydroxide; wherein step (b) comprises altering the product equilibrium to favor the production of bicarbonate products; wherein a quantity of power is required to perform steps (a)-(c), and that power is produced by one or more non-greenhouse-gas emitting power sources.
 27. The method of claim 26, wherein the non-greenhouse-gas emitting power sources are selected from wind-power, hydro-electric power, solar power, and nuclear power. 